High-strength steel sheet excellent in workability and manufacturing method thereof

ABSTRACT

Provided are: a high-strength steel sheet which is improved in both elongation and local formability and thus exhibits excellent workability; and a manufacturing method thereof. The high-strength steel sheet contains C, Si, Mn, Al, P and S with the remainder including iron and unavoidable impurities, and has a metal structure which includes polygonal ferrite, bainite, tempered martensite, and retained austenite. In the metal structure, (1) the bainite has a composite microstructure including both a high-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of 1 μm or more and a low-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of less than 1 μm each identified upon observation with a scanning electron microscope; and (2) the retained austenite is present in a volume percentage of 5% or more of the entire metal structure as determined by a saturation magnetization measurement.

TECHNICAL FIELD

The present invention relates to high-strength steel sheets having excellent workability and having a tensile strength of 780 MPa or more or 590 MPa or more; and methods of manufacturing the steel sheets.

BACKGROUND ART

The automobile industry is facing an urgent need of responding to global environmental issues such as CO₂ emission control. On the other hand, from the viewpoint of securing safety of passengers, the safety standards for collision of automobiles have been made stricter, and structural designing sufficiently securing safety in automobile cabins has been progressing. In order to meet both of these requirements, it is effective to use a high-strength steel sheet having a tensile strength of 780 MPa or more as an automotive structural member and to make the thickness further smaller to reduce the body weight. However, a steel sheet generally exhibits inferior workability with an increasing strength. Application of high-strength steel sheets to automotive members inevitably requires improvement in workability.

Transformation induced plasticity (TRIP)-aided steel sheets (TRIP-aided steel sheets) are known as steel sheets having a strength and workability both at certain levels. A TRIP-aided bainitic ferrite (TBF) steel sheet having a bainitic ferrite matrix and containing retained austenite (hereinafter also referred to as “retained y”) is known as one of TRIP-aided steel sheets (Patent Literature (PTL) 1 to 4). The TBF steel sheet can have a high strength due to the hard bainitic ferrite and an elongation (EL) and a stretch flangeability (λ) both at satisfactory levels due to the fine retained austenite present at the boundary of the bainitic ferrite.

Techniques disclosed in PTL 5 and 6 are known as techniques for increasing the elongation and stretch flangeability to thereby improve the workability. Of these, the technique disclosed in PTL 5 allows the steel sheet to have a higher strength by the action of the martensitic microstructure and to have better workability by forming retained austenite in a predetermined amount. The technique disclosed in PTL 6 allows the steel sheet to have a higher strength by the action of a lower bainitic microstructure and/or a martensitic microstructure and to have better workability by forming retained austenite and tempered martensite in predetermined amounts. The techniques in PTL 5 and 6 control polygonal ferrite area percentage to be 10% or less so as to ensure a tensile strength of 980 MPa or more.

In order to meet both the requirements, it is also effective to use a high-strength steel sheet having a tensile strength of 590 MPa or more as an automotive structural member and to make the thickness further smaller to reduce the body weight. However, a steel sheet generally exhibits inferior workability with an increasing strength as described above. Application of high-strength steel sheets to automotive members inevitably requires improvement in workability.

Dual-phase (DP) steel sheets and TRIP-aided steel sheets are known as steel sheets having a strength and workability both at certain levels. The DP steel sheets have a metal structure including ferrite and martensite. The TRIP-aided steel sheets utilize transformation induced plasticity (TRIP) of retained austenite (retained γ).

A steel sheet disclosed in PTL 7 is known as one of such TRIP-aided steel sheets having a strength and workability both at certain levels. PTL 7 discloses a technique of allowing the steel sheet to have, as a metal structure, a composite microstructure including martensite and retained austenite both present in ferrite and to thereby have a higher strength and better workability (particularly, a higher elongation).

PTL 8 discloses a technique of allowing a TRIP-aided steel sheet to have a better balance between a strength (TS) and an elongation (EL) (specifically, the product of TS and EL) to thereby have better stamping performance. The technique disclosed in this literature allows the steel sheet to have a metal structure including ferrite, retained austenite, and at least one of bainite and martensite so as to have better stamping performance. The literature mentions that the retained austenite functionally improves the steel sheet elongation.

As is disclosed in PTL 7 and PTL 8, a steel sheet, when having a metal structure including retained austenite, can have a strength and elongation properties both at higher levels.

CITATION LIST Patent Literature

-   PTL 1: Japanese Unexamined Patent Application Publication (JP-A) No.     2005-240178 -   PTL 2: JP-A No. 2006-274417 -   PTL 3: JP-A No. 2007-321236 -   PTL 4: JP-A No. 2007-321237 -   PTL 5: JP-A No. 2010-65272 -   PTL 6: JP-A No. 2010-65273 -   PTL 7: JP-A No. 1111-279691 -   PTL 8: JP-A No. 2007-126747

SUMMARY OF INVENTION Technical Problem

Steel sheets for use typically in pillars and members should be subjected to bulging or drawing under more severe conditions, because more and more demands have recently been made on steel sheet workability. To meet this, the steel sheets desirably have further better workability, particularly a further higher elongation. However, it is known that local formability, such as stretch flangeability (λ) and bendability (R), generally deteriorates when the steel sheets have a higher elongation. To prevent this, TRIP-aided steel sheets desirably have better local formability, such as stretch flangeability (λ) and bendability (R), without deterioration in strength and elongation. The aforementioned TRIP-aided steel sheets, however, are disadvantageously poor in local formability, such as stretch flangeability and bendability, because retained austenite transforms into extremely hard martensite during working.

The present invention has been made under these circumstances, and an object thereof is to provide high-strength steel sheets excellent in workability, which have a tensile strength of 780 MPa or more or a tensile strength of 590 MPa or more and have an elongation and local formability both at higher levels. Another object of the present invention is to provide methods of manufacturing the steel sheets.

Solution to Problem

The present invention has achieved the objects and provides, in a first embodiment, a high-strength steel sheet. This high-strength steel sheet contains: C in a content of from 0.10% to 0.3%; Si in a content of from 1.0% to 3.0%; Mn in a content of from 1.5% to 3%; Al in a content of from 0.005% to 3%; P in a content controlled to 0.1% or less; and S in a content controlled to 0.05% or less, in mass percent, with the remainder consisting of iron and inevitable impurities. The steel sheet has a metal structure including bainite, polygonal ferrite, retained austenite, and tempered martensite. (1) When the metal structure is observed with a scanning electron microscope, (1a) the bainite has a composite microstructure including: a high-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of 1 μm or more; and a low-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of less than 1 μm; the high-temperature-formed bainite is present in an area percentage “a” of from 10% to 80% of the entire metal structure; the low-temperature-formed bainite and the tempered martensite are present in a total area percentage “b” of from 10% to 80% of the entire metal structure; and (1b) the polygonal ferrite is present in an area percentage “c” of from 10% to 50% of the entire metal structure. (2) The retained austenite is present in a volume percentage of 5% or more of the entire metal structure as determined by a saturation magnetization measurement. Hereinafter the high-strength steel sheet according to the first embodiment is also referred to as a “first high-strength steel sheet”. The first high-strength steel sheet satisfactorily has a tensile strength of 780 MPa or more.

In a preferred embodiment of the first high-strength steel sheet, when martensite-austenite constituents including both as-quenched martensite and retained austenite are found upon observation at a cross-section of the metal structure with an optical microscope, martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm are present in a number percentage of from 0% to less than 15% of a total number of the entire martensite-austenite constituents at the observed cross-section.

Grains of the polygonal ferrite preferably have an average equivalent circle diameter D of from greater than 0 μm to 10 μm.

The first high-strength steel sheet may further contain one or more elements selected typically from:

(a) Cr in a content of from greater than 0% to 1% and/or Mo in a content of from greater than 0% to 1%;

(b) at least one element selected from the group consisting of Ti in a content of from greater than 0% to 0.15%, Nb in a content of from greater than 0% to 0.15%, and V in a content of from greater than 0% to 0.15%;

(c) Cu in a content of from greater than 0% to 1% and/or Ni in a content of from greater than 0% to 1%;

(d) B in a content of from greater than 0% to 0.005%; and

(e) at least one element selected from the group consisting of Ca in a content of from greater than 0% to 0.01%, Mg in a content of from greater than 0% to 0.01%, and a rare-earth element in a content of from greater than 0% to 0.01%.

The present invention further includes a high-strength hot-dip galvanized steel sheet including the first high-strength steel sheet and, on a surface thereof, a hot-dip galvanized layer; and a high-strength hot-dip galvannealed steel sheet including the first high-strength steel sheet and, on a surface thereof, a hot-dip galvannealed layer.

The first high-strength steel sheet according to the present invention may be manufactured by a method including the steps of heating a steel sheet to a temperature range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.]; holding the steel sheet in the temperature range for 50 seconds or longer; cooling the steel sheet down to an arbitrary temperature T at an average cooling rate of 2° C. or above per second, the temperature T falling within a range specified by Expression (1); holding the steel sheet in the temperature range (temperature range T1) specified by Expression (1) for 10 to 100 seconds; and holding the steel sheet in a temperature range (temperature range T2) specified by Expression (2) for 200 seconds or longer, in this order, Expressions (1) and (2) expressed as follows:

400° C.≦T1(° C.)≦540° C.  (1)

200° C.≦T2(° C.)<400° C.  (2)

The present invention, as having achieved the objects, further provides, in a second embodiment, a high-strength steel sheet. This high-strength steel sheet contains; C in a content of from 0.10% to 0.3%; Si in a content of from 1.0% to 3%; Mn in a content of from 1.0% to 2.5%; Al in a content of from 0.005% to 3%; P in a content controlled to 0.1% or less; and S in a content controlled to 0.05% or less, in mass percent, with the remainder consisting of iron and inevitable impurities. The steel sheet has a metal structure including polygonal ferrite, bainite, tempered martensite, and retained austenite. (1) When the metal structure is observed with a scanning electron microscope, (1a) the polygonal ferrite is present in an area percentage “a” of greater than 50% of the entire metal structure; and (1b) the bainite has a composite microstructure including; a high-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of 1 μm or more; and a low-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of less than 1 μm, the high-temperature-formed bainite is present in an area percentage “b” of from 5% to 40% of the entire metal structure; and the low-temperature-formed bainite and the tempered martensite are present in a total area percentage “c” of from 5% to 40% of the entire metal structure. (2) The retained austenite is present in a volume percentage of 5% or more of the entire metal structure as determined by a saturation magnetization measurement. The high-strength steel sheet according to the second embodiment is hereinafter also referred to as a “second high-strength steel sheet”. The second high-strength steel sheet satisfactorily has a tensile strength of 590 MPa or more.

In a preferred embodiment of the second high-strength steel sheet, when martensite-austenite constituents including both as-quenched martensite and retained austenite are found upon observation at a cross-section of the metal structure with an optical microscope, martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm are present in a number percentage of from 0% to less than 15% of a total number of entire martensite-austenite constituents at the observed cross-section.

Grains of the polygonal ferrite preferably have an average equivalent circle diameter D of from greater than 0 μm to 10 μm.

The second high-strength steel sheet may further contain one or more elements selected typically from:

(a) Cr in a content of from greater than 0% to 1% and/or Mo in a content of from greater than 0% to 1%;

(b) at least one element selected from the group consisting of Ti in a content of from greater than 0% to 0.15%, Nb in a content of from greater than 0% to 0.15%, and V in a content of from greater than 0% to 0.15%;

(c) Cu in a content of from greater than 0% to 1% and/or Ni in a content of from greater than 0% to 1%;

(d) B in a content of from greater than 0% to 0.005%; and

(e) at least one element selected from the group consisting of Ca in a content of from greater than 0% to 0.01%, Mg in a content of from greater than 0% to 0.01%, and a rare-earth element in a content of from greater than 0% to 0.01%.

The present invention further includes a high-strength hot-dip galvanized steel sheet including the second high-strength steel sheet and, on a surface thereof, a hot-dip galvanized layer; and a high-strength hot-dip galvannealed steel sheet including the second high-strength steel sheet and, on a surface thereof, a hot-dip galvannealed layer.

The second high-strength steel sheet according to the present invention may be manufactured by a method including the steps of heating a steel sheet to a temperature range of from [Ac₁ point+20° C.] to [Ac₃ point+20° C.]; holding the steel sheet in the temperature range for 50 seconds or longer; cooling the steel sheet down to an arbitrary temperature T at an average cooling rate of from 2° C. to 50° C. per second, the temperature T falling within a range specified by Expression (1); holding the steel sheet in the temperature range specified by Expression (1) for 10 to 100 seconds; and holding the steel sheet in a temperature range specified by Expression (2) for 200 seconds or longer, in this order, Expressions (1) and (2) expressed as follows:

400° C.≦T1(° C.)≦540° C.  (1)

200° C.≦T2(° C.)<400° C.  (2)

As used herein the term “X and/or Y” refers to that at least one of X and Y is contained.

Advantageous Effects of Invention

The present invention can provide a first high-strength steel sheet, which has elongation and local formability at satisfactory levels and exhibits superior workability even having a high strength of 780 MPa or more. This is achieved by forming, particularly as bainite, both two different bainitic microstructures, i.e., a high-temperature-formed bainite and a low-temperature-formed bainite, and forming polygonal ferrite in a predetermined amount. The high-temperature-formed bainite and the low-temperature-formed bainite differ from each other in existence form of retained austenite and carbides. The high-temperature-formed bainite is formed at a high temperature in the range of from 400° C. to 540° C.; whereas the low-temperature-formed bainite is formed at a low temperature in the range of from 200° C. to lower than 400° C. The present invention can also provide a method of manufacturing the first high-strength steel sheet having a strength and workability both at high levels.

The present invention can further provide a second high-strength steel sheet, which has elongation and local formability at satisfactory levels and exhibits superior workability even having a high strength of 590 MPa or more. This can be achieved by forming polygonal ferrite in an area percentage of greater than 50% of the entire metal structure; and forming, particularly as bainite, both two different bainitic microstructures, i.e., a high-temperature-formed bainite and a low-temperature-formed bainite. The high-temperature-formed bainite and the low-temperature-formed bainite differ from each other in existence form of retained austenite and carbides. The high-temperature-formed bainite is formed at a high temperature in the range of from 400° C. to 540° C.; whereas the low-temperature-formed bainite is formed at a low temperature in the range of from 200° C. to lower than 400° C. The present invention can also provide a method of manufacturing the second high-strength steel sheet having a strength and workability both at high levels.

BRIEF DESCRIPTION OF DRAWINGS

FIG. 1 is a schematic view illustrating an exemplary average distance between adjacent regions of retained austenite and/or carbide.

FIG. 2 are diagrams schematically illustrating how the high-temperature-formed bainite and the low-temperature-formed bainite and a similar microstructure (the low-temperature-formed bainite and tempered martensite) are distributed.

FIG. 3 is a schematic view illustrating an exemplary heat pattern in the temperature range T1 and the temperature range T2.

FIG. 4 is a graph illustrating a relationship between the elongation (EL) and the tensile strength (TS).

FIG. 5 is a graph illustrating a relationship between the elongation (EL) and the tensile strength (TS).

DESCRIPTION OF EMBODIMENTS

Initially, a first high-strength steel sheet according to the present invention will be illustrated.

The present inventors have made intensive investigations to improve the workability, particularly the elongation, and the local formability of a first high-strength steel sheet having a tensile strength of 780 MPa or more. As a result, they have obtained findings (1) to (5) as follows:

(1) There can be provided a first high-strength steel sheet having a higher elongation and better local formability and exhibiting superior workability by:

allowing the steel sheet to have a metal structure as a mixed microstructure including bainite, polygonal ferrite, retained austenite, and tempered martensite; and,

forming, particularly as bainite among these microstructures, two different bainitic microstructures including:

-   -   (1a) a high-temperature-formed bainite having an average         center-to-center distance of 1 μm or more, the center-to-center         distance being between adjacent retained austenite grains,         between adjacent carbide grains, or between a retained austenite         grain and an adjacent carbide (these are hereinafter also         synthetically referred to as “retained austenite or the like”);         and     -   (1b) a low-temperature-formed bainite having an average         center-to-center distance of the retained austenite or the like         of less than 1 μm.

(2) Specifically, the high-temperature-formed bainite contributes to a higher steel sheet elongation; whereas the low-temperature-formed bainite contributes to better steel sheet local formability.

(3) The steel sheet can have a further higher elongation without deterioration in local formability by forming a predetermined amount of polygonal ferrite in the metal structure.

(4) The polygonal ferrite in a predetermined amount can be formed by heating the steel sheet in a ferrite-austenite two-phase temperature range [specifically, in a temperature range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.]].

(5) To form the two different bainitic microstructures in predetermined amounts, the steel sheet may be, after being heated in the two-phase temperature range, cooled down to an arbitrary temperature T in a temperature range of from 400° C. to 540° C. (this temperature range is hereinafter also referred to as a “temperature range T1”) at an average cooling rate of 2° C. or above per second; held in the temperature range T1 for 10 to 100 seconds to form a high-temperature-formed bainite; cooled down to a temperature range of from 200° C. to lower than 400° C. (this temperature range is hereinafter also referred to as a “temperature range T2”); and held in the temperature range T2 for 200 seconds or longer. The present invention has been made based on these findings.

Initially, the metal structure that features in the first high-strength steel sheet according to the present invention will be illustrated.

Metal Structure

The first high-strength steel sheet according to the present invention has a metal structure as a mixed microstructure including bainite, polygonal ferrite, retained austenite, and tempered martensite.

Bainite and Tempered Martensite

Initially, bainite that features prominently in the present invention will be illustrated. As used herein the “bainite” also includes bainitic ferrite. The bainite microstructure includes precipitated carbides, whereas the bainitic ferrite microstructure does not include precipitated carbides.

A feature of the first high-strength steel sheet according to the present invention is that the bainite has a composite microstructure including a high-temperature-formed bainite and a low-temperature-formed bainite having a higher strength than that of the high-temperature-formed bainite. The high-temperature-formed bainite contributes to a higher steel sheet elongation, whereas the low-temperature-formed bainite contributes to better steel sheet local formability. The steel sheet, as including the two different bainitic microstructures, can have a higher elongation while surely having satisfactory local formability and exhibit better workability in general. This is probably because the combination of the bainitic microstructures differing in strength level causes nonuniform deformation and thereby increases the work hardenability.

As used herein the term “high-temperature-formed bainite” refers to a bainitic microstructure that is formed in the temperature range T1 of from 400° C. to 540° C. during a cooling process after heating to a temperature in the range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.] (two-phase temperature range). The high-temperature-formed bainite may be defined as a microstructure having an average distance of the retained austenite or the like of 1 μm or more as determined by subjecting a cross section of the steel sheet to Nital etching and observing the etched cross section with a scanning electron microscope (SEM).

In contrast, the term “low-temperature-formed bainite” refers to a bainitic microstructure that is formed in the temperature range T2 of from 200° C. to lower than 400° C. during the cooling process after heating to the two-phase temperature range. The low-temperature-formed bainite may be defined as a microstructure having an average distance of the retained austenite or the like of less than 1 μm as determined by subjecting a cross section of the steel sheet to Nital etching and observing the etched cross section with a scanning electron microscope (SEM).

As used herein the term “average distance of the retained austenite or the like” refers to an average of center-to-center distances between adjacent retained austenite grains, center-to-center distances between adjacent carbide grains, and center-to-center distances between a retained austenite grain and an adjacent carbide as measured upon SEM observation of the steel sheet cross-section. The term “center-to-center distance” refers to a distance (spacing) between center positions, which center positions are determined on each retained austenite or each carbide upon measurement on most adjacent regions of retained austenite and/or carbide. Each center position is determined by determining a major axis and a minor axis of the retained austenite or carbide and defining a location where the major axis intersects the minor axis as the center position.

When the retained austenite or carbide precipitates at lath boundaries, two or more retained austenite grains and/or two or more carbide grains lie in a row to be in an acicular form or plate form. In this case, as illustrated in FIG. 1, the center-to-center distance may be defined not as a distance between adjacent grains of retained austenite and/or carbide but a spacing between one row and another which rows are formed by the retained austenite and/or carbide grains lying in a row in the major axis direction. This spacing is also referred to as a lath-to-lath distance.

The tempered martensitic microstructure functions similarly to the low-temperature-formed bainite and contributes to better steel sheet local formability. The low-temperature-formed bainite and the tempered martensite are undistinguishable from each other even under SEM observation, and they are herein also synthetically referred to as a “low-temperature-formed bainite or the like”.

The present invention can provide a first high-strength steel sheet being improved in workability in general. This is achieved by allowing the steel sheet to have a composite bainitic microstructure including the high-temperature-formed bainite and the low-temperature-formed bainite or the like. Specifically, the high-temperature-formed bainite is softer than the low-temperature-formed bainite or the like and helps the steel sheet to have a higher elongation (EL) to thereby have better workability. In contrast, the low-temperature-formed bainite or the like is present as small grains of carbides and retained austenite, thereby relieves the stress concentration upon deformation, and helps the steel sheet to have a higher stretch flangeability (λ) and/or a higher bendability (R) and to have better local formability. This contributes to better workability. The first high-strength steel sheet according to the present invention includes both the high-temperature-formed bainite and the low-temperature-formed bainite or the like, thereby has better work hardenability and a higher elongation, and exhibits better workability.

In the present invention, bainitic microstructures are classified as the “high-temperature-formed bainite” and the “the low-temperature-formed bainite or the like” by the differences in the forming temperature range and in the average distance of the retained austenite or the like. This is because the bainitic microstructures are not clearly distinguishable from each other by a general academic structural definition. Typically, lathy bainite and bainitic ferrite are classified as upper bainite and lower bainite by the transformation temperature. However, these microstructures, as well as the martensitic microstructure, are undistinguishable from one another by SEM observation in steels containing Si in a high content of 1.0% or more as in the present invention. This is because carbide precipitation associated with bainitic transformation is suppressed in such steels. According to the present invention, therefore, the bainitic microstructures are classified or distinguished not by the academic structural definition but by the differences in the forming temperature range and in the average distance of the retained austenite or the like.

The high-temperature-formed bainite and the low-temperature-formed bainite or the like may be distributed in any distribution pattern not limited. For example, both the high-temperature-formed bainite and the low-temperature-formed bainite or the like may be present in each prior austenite grain; or the high-temperature-formed bainite and the low-temperature-formed bainite or the like may be formed in different prior austenite grains from each other (in this case, the high-temperature-formed bainite is present in one prior austenite grain, and the low-temperature-formed bainite or the like is present in another prior austenite grain).

FIG. 2 schematically illustrate how the high-temperature-formed bainite and the low-temperature-formed bainite or the like are distributed. In FIG. 2, the high-temperature-formed bainite is hatched, and the low-temperature-formed bainite or the like is finely dotted. FIG. 2( a) illustrates the high-temperature-formed bainite and the low-temperature-formed bainite or the like both present in each prior austenite grain. FIG. 2( b) illustrates the high-temperature-formed bainite present in one prior austenite grain, and the low-temperature-formed bainite or the like present in another. The filled circles illustrated in FIG. 2 represent martensite-austenite constituents, which will be described later.

In an embodiment, the high-temperature-formed bainite is present in an area percentage of “a” of the entire metal structure; and the low-temperature-formed bainite or the like (the low-temperature-formed bainite and tempered martensite) is present in a total area percentage of “b” of the entire metal structure. In this case, the area percentages “a” and “b” should each fall within the range of from 10% to 80%. Not an area percentage of the low-temperature-formed bainite, but a total area percentage of the low-temperature-formed bainite and the tempered martensite is specified herein. This is because these microstructures are undistinguishable from each other by SEM observation.

The area percentage “a” is controlled to the range of from 10% to 80%. The high-temperature-formed bainite, if present in an excessively small amount, may fail to help the steel sheet to have a sufficient elongation and to exhibit better workability. To prevent this, the area percentage “a” is 10% or more, preferably 15% or more, and more preferably 20% or more. However, the high-temperature-formed bainite, if present in an excessively large amount, may fail to exhibit sufficient effects of the combination with the low-temperature-formed bainite or the like. To prevent this, the high-temperature-formed bainite is present in an area percentage “a” of 80% or less, preferably 70% or less, more preferably 60% or less, and furthermore preferably 50% or less.

The total area percentage “b” is controlled to the range of from 10% to 80%. The low-temperature-formed bainite or the like, if present in an excessively small amount, may fail to help the steel sheet to have sufficient local formability and fail to improve the workability. To prevent this, the total area percentage “b” is 10% or more, preferably 15% or more, and more preferably 20% or more. However, the low-temperature-formed bainite or the like, if present in an excessively large amount, may fail to exhibit sufficient effects of the combination with the high-temperature-formed bainite. To prevent this, the low-temperature-formed bainite or the like is present in an area percentage “b” of 80% or less, preferably 70% or less, more preferably 60% or less, and furthermore preferably 50% or less.

The area percentage “a” and the total area percentage “b” may be in any relationship with each other, as long as they fall within the above-specified ranges respectively. All embodiments where “a” is larger than “b”; where “a” is smaller than “b”; and where “a” equals “b” are included herein.

The ratio between the high-temperature-formed bainite and the low-temperature-formed bainite or the like may be determined according to properties required of the steel sheet. Specifically, to further improve the local formability (particularly, the stretch flangeability (λ)) among the steel sheet workability, the ratio of the high-temperature-formed bainite may be minimized, whereas the ratio of the low-temperature-formed bainite or the like may be maximized. To further improve the elongation among the steel sheet workability, the ratio of the high-temperature-formed bainite may be maximized, whereas the ratio of the low-temperature-formed bainite or the like may be minimized. To further increase the steel sheet strength, the ratio of the low-temperature-formed bainite or the like may be maximized, whereas the ratio of the high-temperature-formed bainite may be minimized.

Polygonal Ferrite

The polygonal ferrite microstructure is softer than bainite, functionally increases the steel sheet elongation, and contributes to better workability. To exhibit these actions, the polygonal ferrite is controlled to be present in an area percentage of 10% or more, preferably 12% or more, and more preferably 15% or more, of the entire metal structure. However, the polygonal ferrite, if present in an excessively large amount, may adversely affect the steel sheet strength. To prevent this, the polygonal ferrite is present in an area percentage of 50% or less, preferably 45% or less, and more preferably 40% or less, of the entire metal structure.

The polygonal ferrite grains preferably have an average equivalent circle diameter D of from greater than 0 μm to 10 μm. The steel sheet can have a further higher elongation by having a small average equivalent circle diameter D of the polygonal ferrite grains and allowing the polygonal ferrite to be dispersed as smaller grains. While the detailed mechanism thereof remains unclear, this is probably because the polygonal ferrite refinement allows the polygonal ferrite to be dispersed more uniformly in the entire metal structure, thereby impedes nonuniform deformation, and contributes to a further higher elongation. Specifically, the first high-strength steel sheet according to the present invention has a mixed metal structure including the bainite, polygonal ferrite, retained austenite, and tempered martensite. Owing to this, increasing sizes of the polygonal ferrite grains may cause variation in sizes of respective microstructures. Thus, nonuniform deformation may occur to cause local strain concentration, and this may probably impede improvements in workability (particularly, effective improvement in elongation due to polygonal ferrite formation). To prevent this, the polygonal ferrite grains have an average equivalent circle diameter D of preferably 10 μm or less, more preferably 8 μm or less, furthermore preferably 5 μm or less, and particularly preferably 3 μm or less.

The area percentage and average equivalent circle diameter D of the polygonal ferrite can be measured through SEM observation.

Bainite, Tempered Martensite, and Polygonal Ferrite

In a preferred embodiment of the present invention, the total (a+b+c) of the area percentages “a”, “b”, and “c” is 70% or more of the entire metal structure. The area percentage “a” is an area percentage of the high-temperature-formed bainite. The area percentage “b” is a total area percentage of the low-temperature-formed bainite or the like (the low-temperature-formed bainite and tempered martensite). The area percentage “c” is an area percentage of the polygonal ferrite. The steel sheet, if having a total area percentage (a+b+c) of less than 70%, may have an insufficient elongation. The total area percentage (a+b+c) is more preferably 75% or more and furthermore preferably 80% or more. The upper limit of the total area percentage (a+b+c) may be determined in consideration of the retained austenite volume percentage as determined by a saturation magnetization measurement, and is typically 95%.

Retained Austenite (Retained γ)

The retained austenite transforms to martensite upon deformation of the steel sheet due to stress as received, effectively accelerates the deformed area to be hardened, and prevents strain concentration. This improves the uniform deformability and allows the steel sheet to exhibit a high elongation. These effects are generally known as “TRIP effects”.

To exhibit the effects, the steel sheet contains the retained austenite in a volume percentage of 5% or more of the entire metal structure as determined by a saturation magnetization measurement. The retained austenite may be present in a volume percentage of preferably 8% or more, and more preferably 10% or more. However, the retained austenite, if present in an excessively large amount, may cause excessive formation and resulting coarsening of the martensite-austenite constituents and adversely affect the local formability (stretch flangeability and bendability). To prevent this, the upper limit of the retained austenite volume percentage may be about 30% and preferably 25%.

The retained austenite is predominantly formed between laths in the metal structure, but may be present as blocks as part of the martensite-austenite constituents on lathy microstructure aggregates (e.g., blocks and/or packets) or at the prior austenite grain boundary.

Others

The first high-strength steel sheet according to the present invention has a metal structure including bainite, polygonal ferrite, retained austenite, and tempered martensite as described above. The metal structure may include these microstructures exclusively, but may further include any of other microstructures within ranges not adversely affecting advantageous effects of the present invention. The other microstructures are exemplified by (a) a martensite-austenite constituent including both as-quenched martensite and retained austenite in combination; and (b) pearlite.

(a) Martensite-Austenite Constituent

The martensite-austenite constituent (MA constituent) is generally known as a composite phase of as-quenched martensite (fresh martensite) and retained austenite and is a microstructure formed so that part of a microstructure, which has been present as untransformed austenite before final cooling, transforms to martensite during the final cooling, and the remainder remains as austenite. The resulting martensite-austenite constituent is a very hard microstructure because carbon is enriched to a high concentration in the microstructure during a heat treatment process (particularly, austemper process) and part of the microstructure transforms to a martensitic microstructure. Because of large difference in hardness from the bainite, the martensite-austenite constituent may readily cause voids as a result of stress concentration thereon during deformation. The martensite-austenite constituent, if present in an excessively large amount, may cause the steel sheet to have insufficient stretch flangeability and/or bendability, resulting in insufficient local formability. The martensite-austenite constituent, if present in an excessively large amount, may readily cause the steel sheet to have an excessively high strength. The martensite-austenite constituent more readily forms with an increasing retained austenite amount and an increasing Si content. The amount of the formed martensite-austenite constituent is preferably minimized.

The metal structure may include the martensite-austenite constituents in an area percentage of preferably 30% or less, more preferably 25% or less, and furthermore preferably 20% or less, of the entire metal structure upon observation of the metal structure with an optical microscope.

In a preferred embodiment, martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm are present in a number percentage of from 0% to less than 15% of the total number of the entire martensite-austenite constituents. Such coarse martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm may adversely affect the local formability. The number percentage of the martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm is more preferably less than 10% and furthermore preferably less than 5% of the total number of the entire martensite-austenite constituents.

The number percentage of the martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm may be determined under observation of a surface of a cross-section in parallel to the rolling direction with an optical microscope.

The martensite-austenite constituents are recommended to be minimized in size because it has been experimentally demonstrated that martensite-austenite constituents, when having large grain sizes, may readily cause void formation.

(b) Pearlite

In a preferred embodiment, the metal structure may include the pearlite in an area percentage of 20% or less of the entire metal structure upon SEM observation of the metal structure. The pearlite, if contained in an area percentage of greater than 20%, may cause the steel sheet to have an insufficient elongation, and this may impede improvements in workability. The area percentage of the pearlite is more preferably 15% or less, furthermore preferably 10% or less, and particularly preferably 5% or less of the entire metal structure.

The metal structure may be determined or measured by procedures as follows.

The high-temperature-formed bainite, the low-temperature-formed bainite or the like (the low-temperature-formed bainite and tempered martensite), polygonal ferrite, and pearlite may be identified by subjecting a cross-section parallel to the steel sheet rolling direction at a depth of one-fourth the sheet thickness to Nital etching, and observing the etched cross-section with a SEM at a magnification of about 3000 times.

The high-temperature-formed bainite and the low-temperature-formed bainite or the like are observed mainly as gray microstructures, in which the retained austenite or the like is dispersed in the grains. The retained austenite or the like is observed as a white or pale gray microstructure. Upon SEM observation, the high-temperature-formed bainite and the low-temperature-formed bainite or the like are therefore observed as including the retained austenite and carbides, and the area percentage thereof is calculated as one including the retained austenite or the like. The polygonal ferrite is observed as grains that do not include the retained austenite or the like. The retained austenite or the like, if present, is observed as a white or pale gray microstructure as described above. The pearlite is observed as a layered microstructure including both carbides and ferrite.

When the steel sheet cross-section is etched with a Nital solution, the carbide and the retained austenite are observed both as white or pale gray microstructures and are undistinguishable from each other. Among them, the carbide (e.g., cementite) tends to precipitate in laths rather than between laths when formed in a lower temperature range. Based on this, the carbide grains, when dispersed with a large spacing, may be considered to be formed in a high temperature range; and, when dispersed with a small spacing, may be considered to be formed in a low temperature range. The retained austenite is generally formed between laths. Such laths have smaller sizes with a decreasing forming temperature of the microstructure. Based on this, the retained austenite microstructures, when dispersed with a large spacing, may be considered to be formed in a high temperature range; and, when dispersed with a small spacing, may be considered to be formed in a low temperature range. The present invention therefore focuses attention on retained austenite or the like, which is observed as a white or pale gray microstructure in an observation view field upon SEM observation of a Nital-etched cross section of the steel sheet. Assume that center-to-center distances of adjacent retained austenite or the like are measured, and the measured distances are averaged to give an average (average center-to-center distance). A microstructure having the average (average distance) of 1 μm or more is defined herein as a high-temperature-formed bainite; whereas a microstructure having the average (average distance) of less than 1 μm is defined as a low-temperature-formed bainite or the like.

The retained austenite microstructure is unidentifiable by SEM observation, and the volume percentage thereof is determined by a saturation magnetization measurement. The measured volume percentage can be read as an “area percentage” thereof without modification. A detailed measurement principle of the saturation magnetization measurement may be found in “R&D KOBE STEEL ENGINEERING REPORTS, Vol. 52, Sample No. 3, 2002, p. 43-46”.

As has been described above, the volume percentage (area percentage) of the retained austenite is determined by a saturation magnetization measurement, whereas the area percentages of other microstructures such as the high-temperature-formed bainite are measured through SEM observation as including the retained austenite. The total of these area percentages may therefore exceed 100%.

The martensite-austenite constituents may be observed as white microstructures by subjecting a cross-section parallel to the steel sheet rolling direction at a depth one-fourth the sheet thickness to Nital etching, and observing the etched cross-section with an optical microscope at a magnification of about 1000 times.

Next, a chemical composition of the first high-strength steel sheet according to the present invention will be illustrated.

Chemical Composition

The first high-strength steel sheet according to the present invention satisfactorily contains C in a content of from 0.10% to 0.3%; Si in a content of from 1.0% to 3.0%; Mn in a content of from 1.5% to 3%; and Al in a content of from 0.005% to 3% and is controlled to contain P in a content of from greater than 0% to 0.1%; and S in a content of from greater than 0% to 0.05%.

Carbon (C) element essentially helps the steel sheet to have a higher strength and allows the formation of retained austenite. For this reason, the carbon content is controlled to 0.10% or more, preferably 0.13% or more, and more preferably 0.15% or more. However, carbon, if contained in excess, may cause the steel sheet to have insufficient weldability. To prevent this, the carbon content is controlled to 0.3% or less, preferably 0.25% or less, and more preferably 0.20% or less.

Silicon (Si) element acts as a solute strengthening element, extremely importantly contributes to a higher strength of the steel sheet, suppresses precipitation of carbides during holding in the after-mentioned temperature range T1 and in the temperature range T2 (during austemper process), and thereby allows effective formation of the retained austenite. For these reasons, the Si content is controlled to 1.0% or more, preferably 1.2% or more, and more preferably 1.3% or more. However, Si, if contained in excess, may impede reverse transformation to the austenite phase during heating/soaking in annealing, and this may cause the steel sheet to have an insufficient strength due to a large amount of residual polygonal ferrite. The excess Si may also cause silicon scales on the steel sheet surface during hot rolling and cause the steel sheet to have poor surface quality. To prevent this, the Si content is controlled to 3.0% or less, preferably 2.5% or less, and more preferably 2.0% or less.

Manganese (Mn) element is necessary for obtaining bainite and tempered martensite. The Mn element also effectively functionally stabilizes austenite (γ) to form the retained austenite. To exhibit these actions, the Mn content is controlled to 1.5% or more, preferably 1.8% or more, and more preferably 2.0% or more. However, Mn, if contained in excess, may remarkably impede the formation of the high-temperature-formed bainite. Such excess Mn may also cause deterioration in weldability and in workability due to segregation. To prevent this, the Mn content is controlled to 3% or less, preferably 2.8% or less, and more preferably 2.7% or less.

Aluminum (Al) element suppresses the precipitation of carbides during the austemper process and contributes to the formation of the retained austenite, as with Si. The Al element also acts as a deoxidizer during a steel-making process. For these reasons, the Al content is controlled to 0.005% or more, preferably 0.01% or more, and more preferably 0.03% or more. However, Al, if contained in excess, may cause the steel sheet to contain excessively large amounts of inclusions to thereby have insufficient ductility. To prevent this, the Al content is controlled to 3% or less, preferably 1.5% or less, more preferably 1% or less, and furthermore preferably 0.5% or less.

Phosphorus (P) element is an impurity to be inevitably contained in the steel. Phosphorus, if contained in excess, may cause the steel sheet to have insufficient weldability. To prevent this, the phosphorus content is controlled to 0.1% or less, preferably 0.08% or less, and more preferably 0.05% or less. The phosphorus content is desirably minimized, but is industrially hardly reduced to 0%.

Sulfur (S) element is an impurity to be inevitably contained in the steel and adversely affects the steel sheet weldability as with phosphorus. Sulfur forms sulfide inclusions in the steel sheet, and large amounts of such sulfide inclusions may adversely affect the weldability. To prevent this, the sulfur content is controlled to 0.05% or less, preferably 0.01% or less, and more preferably 0.005% or less. The sulfur content is desirably minimized, but is industrially hardly reduced to 0%.

The first high-strength steel sheet according to the present invention has a chemical composition within the above-specified ranges, with the remainder consisting of iron and inevitable impurities other than P and S. The inevitable impurities are exemplified by N (nitrogen), O (oxygen), and tramp elements (e.g., Pb, Bi, Sb, and Sn). Of the inevitable impurities, the content of nitrogen is preferably from greater than 0% to 0.01%, and the content of oxygen is preferably from greater than 0% to 0.01%.

Nitrogen (N) element precipitates as nitrides in the steel sheet and contributes to the steel sheet strengthening. However, nitrogen, if contained in excess, may cause precipitation of nitrides in large amounts and cause the steel sheet to deteriorate in elongation, stretch flangeability, and bendability. To prevent this, the nitrogen content is preferably 0.01% or less, more preferably 0.008% or less, and furthermore preferably 0.005% or less.

Oxygen (O) element, if contained in excess, may cause deterioration in elongation, stretch flangeability, and bendability. To prevent this, the oxygen content is preferably 0.01% or less, more preferably 0.005% or less, and furthermore preferably 0.003% or less.

The first high-strength steel sheet according to the present invention may further contain at least one element selected typically from:

(a) Cr in a content of from greater than 0% to 1% and/or Mo in a content of from greater than 0% to 1%;

(b) at least one element selected from the group consisting of Ti in a content of from greater than 0% to 0.15%, Nb in a content of from greater than 0% to 0.15%, and V in a content of from greater than 0% to 0.15%;

(c) Cu in a content of from greater than 0% to 1% and/or Ni in a content of from greater than 0% to 1%;

(d) B in a content of from greater than 0% to 0.005%; and

(e) at least one element selected from the group consisting of Ca in a content of from greater than 0% to 0.01%, Mg in a content of from greater than 0% to 0.01%, and a rare-earth element in a content of from greater than 0% to 0.01%.

(a) Chromium (Cr) and molybdenum (Mo) elements effectively contribute to the formation of bainite and tempered martensite, as with Mn as mentioned above. Each of these elements may be used alone or in combination. To exhibit these actions effectively, Cr and Mo may be contained separately in a content of preferably 0.1% or more and more preferably 0.2% or more. However, Cr and Mo, if separately contained in a content of more than 1%, may remarkably impede the formation of the high-temperature-formed bainite. Such excessive addition may also cause a higher cost. To prevent these, the Cr and Mo contents are each preferably 1% or less, more preferably 0.8% or less, and furthermore preferably 0.5% or less. A total content of Cr and Mo, when used in combination, is recommended to be 1.5% or less.

(b) Titanium (Ti), niobium (Nb), and vanadium (V) elements form carbides, nitrides, and other precipitates in the steel sheet to strengthen the steel sheet and induce the refinement of prior austenite grains, thus contributing to the refinement of polygonal ferrite grains. To exhibit the actions effectively, Ti, Nb, and V may be contained each in a content of preferably 0.01% or more and more preferably 0.02% or more. However, these elements, if contained in excess, may cause the precipitation of carbides at grain boundaries and cause the steel sheet to have stretch flangeability and/or bendability at insufficient level. To prevent this, the Ti, Nb, and V contents are each preferably 0.15% or less, more preferably 0.12% or less, and furthermore preferably 0.1% or less. Each of Ti, Nb, and V may be contained alone or in combination as a mixture of arbitrary two or more elements.

(c) Copper (Cu) and nickel (Ni) elements effectively stabilize austenite to form retained austenite. Each of these elements may be used alone or in combination. To exhibit the actions effectively, Cu and Ni may be contained each in a content of preferably 0.05% or more and more preferably 0.1% or more. However, Cu and Ni, if contained in excess, may adversely affect the hot workability. To prevent this, the Cu and Ni contents are each preferably 1% or less, more preferably 0.8% or less, and furthermore preferably 0.5% or less. Cu, if contained alone in a content of greater than 1%, may cause deterioration in hot workability. A combination use of Cu with Ni, however, suppresses the deterioration in hot workability. In this combination use, Cu may be added in a content of greater than 1%, though resulting in a higher cost.

(d) Boron (B) element effectively contributes to the formation of bainite and tempered martensite, as with Mn, Cr, and Mo. To exhibit the actions effectively, boron may be contained in a content of preferably 0.0005% or more and more preferably 0.001% or more. However, boron, if contained in excess, may form borides in the steel sheet to impair the ductility. Such excessive boron may also remarkably impede the formation of the high-temperature-formed bainite, as with Cr and Mo. To prevent this, boron may be contained in a content of preferably 0.005% or less, more preferably 0.004% or less, and furthermore preferably 0.003% or less.

(e) Calcium (Ca), magnesium (Mg), and rare-earth elements (REMs) functionally allow inclusions to be finely dispersed in the steel sheet. To exhibit the actions effectively, Ca, Mg, and a rare-earth element may be contained each in a content of preferably 0.0005% or more and more preferably 0.001% or more. However, these elements, if contained in excess, may adversely affect the castability and the hot workability, and this may impede steel sheet manufacturing. Such excess elements may also cause deterioration in steel sheet ductility. To prevent this, the contents of Ca, Mg, and rare-earth elements are controlled each to preferably 0.01% or less, more preferably 0.005% or less, and furthermore preferably 0.003% or less.

As used herein the term “rare-earth element(s)” refers to and includes lanthanoid elements (fifteen elements ranging from La to Lu) as well as Sc (scandium) and Y (yttrium). Of these elements, at least one element selected from the group consisting of La, Ce, and Y is preferred, of which La and/or Ce is more preferred.

The first high-strength steel sheet according to the present invention has a tensile strength of 780 MPa or more, has local formability and an elongation at satisfactory levels, and exhibits excellent workability. The first high-strength steel sheet is advantageously used as materials for automotive structural parts. The automotive structural parts are exemplified by bumping parts such as front and rear side members and crush boxes; as well as pillars and other reinforcing members (e.g., center-pillar reinforcements); roof rail reinforcing members; side sills, floor members, kick-up parts, and other body-constituting parts; shock absorbing parts such as bumper reinforcing members and door impact beams; and seat parts.

The first high-strength steel sheet also has good warm workability and is advantageously usable as materials for warm forming. The term “warm working (warm forming)” refers to forming or shaping in a temperature range of from about 50° C. to about 500° C.

The metal structure and the chemical composition of the first high-strength steel sheet according to the present invention have been described above.

Next, a method capable of manufacturing the first high-strength steel sheet will be illustrated. The first high-strength steel sheet can be manufactured by a method including the steps of heating a steel sheet to a temperature range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.] (two-phase temperature range), the steel sheet having a chemical composition within the above specified ranges; holding the steel sheet in the temperature range for 50 seconds or longer; cooling the steel sheet down to an arbitrary temperature T at an average cooling rate of 2° C. or above per second, the temperature T falling within the range specified by Expression (1); holding the steel sheet in the temperature range specified by Expression (1) for 10 to 100 seconds; and holding the steel sheet in a temperature range specified by Expression (2) for 200 seconds or longer, in this order. The respective steps will be illustrated in order below. Expressions (1) and (2) are expressed as follows:

400° C.≦T1(° C.)≦540° C.  (1)

200° C.≦T2(° C.)<400° C.  (2)

Initially, a high-strength steel sheet is prepared by hot-rolling a slab according to a common procedure to give a hot-rolled steel sheet; and cold-rolling the hot-rolled steel sheet. This is prepared as a high-strength steel sheet to be heated to the two-phase temperature range [temperature range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.]]. The hot rolling may be performed at a finishing mill delivery temperature of typically 800° C. or higher and a coiling temperature of typically 700° C. or lower. The cold rolling may be performed to a cold rolling reduction in a range of typically from 10% to 70%.

The cold-rolled steel sheet obtained through cold rolling is heated to the temperature range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.] and held in the temperature range for 50 seconds or longer for soaking in a continuous annealing line.

The heating to a temperature falling within the ferrite-austenite two-phase temperature range allows the polygonal ferrite formation in a predetermined amount. Specifically, heating to an excessively high temperature may cause the steel sheet to have a temperature falling within the austenite single-phase range, thereby suppress the formation of polygonal ferrite, and cause the steel sheet to fail to have a higher elongation and better workability. To prevent this, the heating temperature is controlled to [Ac₃ point+20° C.] or lower, preferably [Ac₃ point+10° C.] or lower, and more preferably lower than the Ac₃ point. The steel sheet, when heated to a temperature equal to or higher than the Ac₃ point, has a temperature falling within the austenite single-phase temperature range. However, when heating is performed to a temperature of equal to or lower than [Ac₃ point+20° C.], a small amount of polygonal ferrite can remain even after soaking (holding) for a duration on the order of the soaking time as specified in the present invention. Thus, a predetermined amount of polygonal ferrite can be formed by regulating the average cooling rate after soaking as mentioned later. In contrast, heating performed to a temperature of lower than [{(Ac₁ point+Ac₃ point)/2}+20° C.] may cause the formation of polygonal ferrite in an excessively large area percentage of more than 50%, and this may inhibit the steel sheet from surely having a desired strength. To prevent this, the heating temperature is controlled to [{(Ac₁ point+Ac₃ point)/2}+20° C.] or higher, preferably [{(Ac₁ point+Ac₃ point)/2}+30° C.] or higher, and more preferably [{(Ac₁ point+Ac₃ point)/2}+50° C.] or higher.

Soaking in the two-phase temperature range, if performed for a time of shorter than 50 seconds, may fail to heat the steel sheet uniformly, and this may impede the formation of the retained austenite and cause the steel sheet to have an elongation and local formability at insufficient levels and to exhibit unsatisfactory workability. To prevent this, the soaking time is controlled to 50 seconds or longer and preferably 100 seconds or longer. However, soaking, if performed for an excessively long time, may cause the austenite grains to have larger sizes, sequentially cause the polygonal ferrite grains to have larger sizes, and readily cause the steel sheet to have an elongation and local formability at insufficient levels. To prevent this, the soaking time is preferably 500 seconds or shorter and more preferably 450 seconds or shorter.

The heating of the cold-rolled steel sheet to the two-phase temperature range may be performed at an average heating rate of typically 1° C. or above per second.

The Ac₁ point and the Ac₃ point can be calculated from following Expressions (a) and (b), which are described in “Leslie Tekko Zairyo Kagaku (in Japanese; translation of “The Physical Metallurgy of Steels” by Leslie)”, Maruzen Co., Ltd., May 31, 1985, p. 273. In Expressions (a) and (b), a numerical value in brackets represents the content (in mass percent) of each element. When an element is not contained in the steel sheet, calculation can be performed while making the content of the element be 0% (in mass percent). Expressions (a) and (b) are expressed as follows:

Ac ₁(° C.)=723−10.7×[Mn]−16.9×[Ni]+29.1×[Si]+16.9×[Cr]  (a)

Ac ₃(° C.)=910−203×[C]^(1/2)+44.7×[Si]−30×[Mn]−11×[Cr]+31.5×[Mo]−20×[Cu]−15.2×[Ni]+400×[Ti]+104×[V]+700×[P]+400×[Al]  (b)

After being heated to the two-phase temperature range and held in the range for 50 seconds or longer for soaking, the steel sheet is cooled down to an arbitrary temperature T at an average cooling rate of 2° C. or above per second. The temperature T falls within a range specified by Expression (1). Thus, the steel sheet is cooled at an average cooling rate at the predetermined level or higher in a temperature range of from the two-phase temperature range down to the arbitrary temperature T falling within the range specified by Expression (1). This allows the formation of polygonal ferrite in a predetermined amount and allows the formation of both the high-temperature-formed bainite and the low-temperature-formed bainite or the like. Cooling in this temperature range, if performed at an average cooling rate of lower than 2° C. per second, may cause pearlite transformation to form pearlite in excess, and this may cause the steel sheet to have an insufficient elongation and to exhibit unsatisfactory workability. The average cooling rate in this temperature range is preferably 5° C. or above per second, and more preferably 10° C. or above per second. The upper limit of the average cooling rate in this temperature range is not critical, but may be typically about 100° C. per second, because cooling, if performed at an excessively high average cooling rate, may impede the temperature control.

After being cooled down to the arbitrary temperature T falling within the range specified by Expression (1), the steel sheet is held in the temperature range T1 specified by Expression (1) for 10 to 100 seconds, and then held in the temperature range T2 specified by Expression (2) for 200 seconds or longer. Suitable separate controls of the holding times in the temperature range T1 and in the temperature range T2 allow the formation of predetermined amounts of the high-temperature-formed bainite and the low-temperature-formed bainite or the like, respectively. Specifically, holding of the steel sheet in the temperature range T1 for a predetermined time enables the control of the amount of the high-temperature-formed bainite. The austemper process of holding the steel sheet in the temperature range T2 for a predetermined time allows untransformed austenite to transform to the low-temperature-formed bainite or martensite and allows carbon to be enriched in austenite to form retained austenite. This gives a metal structure as specified in the present invention.

The combination of holding in the temperature range T1 and holding in the temperature range T2 also effectively suppresses the formation of martensite-austenite constituents. A mechanism of this is probably as follows. Si and Al, when added, generally suppress carbide precipitation. This allows the presence of free carbon in the steel and induces a phenomenon during the austemper process, in which the free carbon is enriched in the untransformed austenite along with bainitic transformation. The enrichment of carbon in the untransformed austenite allows the retained austenite to be formed in a large amount.

The phenomenon, in which carbon is enriched in the untransformed austenite, will be described below. It is known that the amount of enriched carbon is limited to the content indicated by a T₀ curve where free energy of the ferrite and austenite becomes equal, and therefore bainitic transformation also stops. The T₀ curve shifts to the lower carbon content side with an elevating temperature. When an austemper process is performed at a relatively high temperature, bainitic transformation comes to stop at a certain degree even if the process time is made long. At this time, coarse martensite-austenite constituents are formed due to poor stability of the untransformed austenite.

In consideration of this, the steel sheet is held in the temperature range T2 after being held in the temperature range T1 according to the present invention. This allows carbon to be enriched in a larger content in the untransformed austenite. This also allows the bainitic transformation to proceed more in a low temperature range than in a high temperature range and helps the martensite-austenite constituents to be smaller. Lathy microstructures become smaller in size in the case of holding the steel sheet in the temperature range T2 than in the case of holding the steel sheet in the temperature range T1. This helps the martensite-austenite constituents themselves, even when present, to be finely divided. In addition, the high-temperature-formed bainite has already been formed at the time when holding of the steel sheet in the temperature range T2 starts, because the steel sheet is held in the temperature range T2 after being held in the temperature range T1 for a predetermined time. The high-temperature-formed bainite triggers and accelerates the transformation of the low-temperature-formed bainite in the temperature range T2, and this advantageously effectively shortens the austemper process time.

The size reduction of the lathy microstructures and resulting size reduction of the martensite-austenite constituents can also be achieved by a simple austemper process of holding a steel sheet at a low temperature. In the simple austemper process, the steel sheet is not held in the temperature range T1 but cooled from the two-phase temperature range directly to an arbitrary temperature falling within the range specified by Expression (2) and held only in the temperature range T2 specified by Expression (2). In this process, however, the high-temperature-formed bainite is little formed, and the lathy microstructure in the matrix have a large dislocation density because the steel sheet is not held in the temperature range T1. The resulting steel sheet has an elongation and local formability at insufficient levels and exhibits poor workability.

The temperature range T1 specified by Expression (1) herein specifically ranges from 400° C. to 540° C. Holding of the steel sheet in the temperature range for a predetermined time allows the high-temperature-formed bainite to be formed. Specifically, holding of the steel sheet, if performed at a temperature of higher than 540° C., may suppress the formation the high-temperature-formed bainite, but cause excessive formation of polygonal ferrite and formation of pseudo-pearlite. The resulting steel sheet fails to have desired properties. To prevent this, the upper limit of the temperature range T1 is controlled to 540° C., preferably 520° C., and more preferably 500° C. In contrast, holding of the steel sheet, if performed at a temperature of lower than 400° C., may fail to induce the formation of the high-temperature-formed bainite and cause the steel sheet to have an insufficient elongation and to exhibit unsatisfactory workability. To prevent this, the lower limit of the temperature range T1 is controlled to 400° C. and preferably 420° C.

The steel sheet is held in the temperature range T1 for a holding time of from 10 to 100 seconds. The holding, if performed for a holding time of longer than 100 seconds, may cause excessive formation of the high-temperature-formed bainite, and this may impede the formation of a sufficient amount of the low-temperature-formed bainite or the like even when the steel sheet is subsequently held in the temperature range T2 for a predetermined time in a manner described later. This may cause the steel sheet to fail to have a strength and workability both at satisfactory levels. Such long-term holding in the temperature range T1 may also cause excessive enrichment of carbon in the austenite. This may cause the formation of coarse martensite-austenite constituents even when the austemper process is performed in the temperature range T2 and cause the steel sheet to exhibit poor workability. To prevent this, the holding time is controlled to 100 seconds or shorter, preferably 90 seconds or shorter, and more preferably 80 seconds or shorter. However, holding in the temperature range T1, if performed for an excessively short time, may cause the high-temperature-formed bainite to be formed in a smaller amount. This may cause the steel sheet to have an insufficient elongation and to exhibit unsatisfactory workability. To prevent this, the holding time in the temperature range T1 is controlled to 10 seconds or longer, preferably 15 seconds or longer, more preferably 20 seconds or longer, and furthermore preferably 30 seconds or longer.

As used herein the term “holding time in the temperature range T1” refers to a time (duration) from the time point when the steel sheet surface temperature reaches the upper limit temperature of the temperature range T1 to the time point when the steel sheet surface temperature reaches the lower limit temperature of the temperature range T1. Specifically, the term refers to a time from the time point when steel sheet surface temperature reaches 540° C. to the time point when it reaches 400° C.

To hold the steel sheet in the temperature range T1 specified by Expression (1), any of heat patterns (i), (ii), and (iii) illustrated in FIG. 3 may be employed.

The heat pattern (i) in FIG. 3 is an embodiment, in which the steel sheet is rapidly cooled from the two-phase temperature range down to an arbitrary temperature T falling within the range specified by Expression (1) and is then isothermally held at the temperature T for a predetermined time. After being isothermally held, the steel sheet is cooled down to an arbitrary temperature falling within the range specified by Expression (2). The heat pattern (i) in FIG. 3 illustrates a one-stage isothermal holding. Isothermal holding, however, is not limited to this, and an isothermal holding in two or more stages at different holding temperatures may also be performed, as long as the steel sheet surface temperature fall within the temperature range T1.

The heat pattern (ii) in FIG. 3 is an embodiment, in which the steel sheet is rapidly cooled from the two-phase temperature range down to an arbitrary temperature T falling within the range specified by Expression (1), then cooled in the temperature range T1 at a changed cooling rate over a predetermined time, and cooled down to an arbitrary temperature falling within the range specified by Expression (2) at a further changed cooling rate. The heat pattern (ii) in FIG. 3 illustrates an embodiment where the steel sheet is cooled in the temperature range T1 over a predetermined time. The heat pattern in the present invention is not limited to this, and the process may further include the step of heating over a predetermined time or may further include the step of suitably repeating cooling and heating, as long as the steel sheet surface temperature fall within the temperature range T1. Instead of a one-stage cooling as in the heat pattern (ii) in FIG. 3, a multistage cooling, in which cooling is performed in two or more stages at different cooling rates, may be employed. A one-stage heating or a multistage heating (two or more stages) may also be performed (not shown).

The heat pattern (iii) in FIG. 3 is an embodiment, in which the steel sheet is rapidly cooled from the two-phase temperature range down to an arbitrary temperature T falling within the range specified by Expression (1) and is then slowly cooled down to an arbitrary temperature falling within the range specified by Expression (2) at a changed but constant cooling rate. Even such slow cooling is accepted herein, as long as the residence time of the steel sheet within the temperature range T1 be from 10 to 100 seconds.

The present invention is not limited to the heat patterns (i) to (iii) illustrated in FIG. 3, but can also employ any of other heat patterns than above, as long as the conditions specified herein be satisfied.

The temperature range T2 herein specified by Expression (2) is specifically from 200° C. to lower than 400° C. Holding the steel sheet in the temperature range for a predetermined time allows the untransformed austenite, which has not transformed in the temperature range T1, to transform to the low-temperature-formed bainite, or martensite. The holding performed for such a sufficient holding time allows the bainitic transformation to proceed, gives the retained austenite finally, and allows the martensite-austenite constituents to be finer. The martensite is present as as-quenched martensite immediately after transformation, but is tempered during holding in the temperature range T2, and remains as tempered martensite. The tempered martensite has properties similar to those of the low-temperature-formed bainite that is formed in such a temperature range where martensitic transformation occurs. However, holding at a temperature of 400° C. or higher may cause the formation of coarse martensite-austenite constituents, and this may cause the steel sheet to have an elongation and local formability at insufficient levels and to fail to exhibit better workability. To prevent this, the temperature range T2 is set to lower than 400° C., preferably 390° C. or lower, and more preferably 380° C. or lower. In contrast, holding at a temperature lower than 200° C. may impede the formation of the low-temperature-formed bainite, and this may invite a low carbon content in the austenite, an insufficient amount of the retained austenite, and a larger amount of as-quenched martensite. The resulting steel sheet may thereby have an excessively high strength and have an insufficient elongation and poor local formability. The steel sheet may also fail to have a higher elongation due to the low carton content in the austenite and the insufficient amount of the retained austenite. To prevent these, the lower limit of the temperature range T2 is controlled to 200° C., preferably 250° C., and more preferably 280° C.

The steel sheet is held in the temperature range T2 specified by Expression (2) for a time of 200 seconds or longer. The holding, if performed for a time of shorter than 200 seconds, may cause the low-temperature-formed bainite or the like to be formed in an insufficient amount, and this may invite a low carbon content in the austenite, an insufficient amount of the retained austenite, and a larger amount of the as-quenched martensite. The resulting steel sheet may thereby have an excessively high strength and have an insufficient elongation and poor local formability. The steel sheet may fail to have a higher elongation due to the low carton content in the austenite and the insufficient amount of the retained austenite. The steel sheet may fail to have better local formability because the martensite-austenite constituents formed in the temperature range T1 are not refined (not become smaller). To prevent these, the holding time is controlled to 200 seconds or longer, preferably 250 seconds or longer, and more preferably 300 seconds or longer. Though the upper limit of the holding time is not critical, holding, if performed for an excessively long time, may induce poor productivity and cause the enriched carbon to precipitate as carbides. This may impede the formation of retained austenite and cause the steel sheet to have a low elongation and poor workability. To prevent these, the upper limit of the holding time may be set typically to 1800 seconds.

As used herein the term “holding time in the temperature range T2” refers to a time (duration) from the time point at which the steel sheet surface temperature reaches the upper limit temperature of the temperature range T2 to the time point at which the steel sheet surface temperature reaches the lower limit temperature of the temperature range T2. Specifically, the term refers to a time from the time point at which the surface temperature reaches lower than 400° C. to the time point at which it reaches 200° C.

A way to hold the steel sheet in the temperature range T2 is not limited, as long as the residence time of the steel sheet in the temperature range T2 be 200 seconds or longer. As in the heat patterns in the temperature range T1, the steel sheet may be isothermally held (held at a constant temperature), or may be cooled and/or heated within the temperature range T2. A multistage holding at different holding temperatures may also be employed.

After being held in the temperature range T2 for a predetermined time, the steel sheet is cooled down to room temperature and yields a first high-strength steel sheet according to the present invention.

The first high-strength steel sheet may bear a hot-dip galvanized layer or a hot-dip galvannealed layer on a surface thereof.

The hot-dip galvanized layer or the hot-dip galvannealed layer may be formed under any conditions not limited, such as known conditions.

Typically, the hot-dip galvanized layer may be formed at a plating bath temperature of preferably from 400° C. to 500° C. and more preferably from 440° C. to 470° C. The plating bath may have any chemical composition not limited, and a known hot-dip galvanization bath can be employed.

A hot-dip galvannealed steel sheet may be manufactured by subjecting a hot-dip galvanized steel sheet bearing a hot-dip galvanized layer to an alloying treatment according to a common procedure. The alloying treatment may be performed typically by holding the hot-dip galvanized steel sheet at a temperature of typically from about 450° C. to about 600° C. (particularly preferably from about 480° C. to about 570° C.) for a duration of from about 5 to about 30 seconds (particularly preferably from about 10 to about 25 seconds). The alloying treatment may be performed typically with a heating furnace, a direct fire, or an infrared heating furnace. The heating process is also not limited and is exemplified by gas heating, induction heater heating (heating with induction heating equipment), or another customary process.

The technique according to the present invention is advantageously applied particularly to thin steel sheets having a thickness of 3 mm or less.

The first high-strength steel sheet according to the present invention has been described above.

Next, a second high-strength steel sheet according to the present invention will be illustrated.

The present inventors have made intensive investigations to improve the workability, particularly elongation, and local formability of a second high-strength steel sheet having a tensile strength of 590 MPa or more. As a result, they have obtained findings (1) to (3) as follows:

(1) There can be provided a second high-strength steel sheet having better local formability without deterioration in elongation and exhibiting superior workability by:

allowing the steel sheet to have a metal structure mainly including polygonal ferrite (specifically, including polygonal ferrite in an area percentage of greater than 50% of the entire metal structure) and being a mixed microstructure further including bainite, tempered martensite, and retained austenite, and

forming, particularly as bainite, two different microstructures including:

-   -   (1a) a high-temperature-formed bainite having an average         center-to-center distance of 1 μm or more, the center-to-center         distance being between adjacent retained austenite grains,         between adjacent carbide grains, or between a retained austenite         grain and an adjacent carbide grain (these are hereinafter also         synthetically referred to as “retained austenite or the like”);         and     -   (1b) a low-temperature-formed bainite having an average         center-to-center distance of the retained austenite or the like         of less than 1 μm.

(2) Specifically, the high-temperature-formed bainite contributes to a higher steel sheet elongation; whereas the low-temperature-formed bainite contributes to better steel sheet local formability.

(3) To form the two different bainitic microstructures in predetermined amounts, the steel sheet may be, after being heated in the two-phase temperature range, cooled down to an arbitrary temperature T in a temperature range of from 400° C. to 540° C. (this temperature range is hereinafter also referred to as a “temperature range T1”) at an average cooling rate of 2° C. or above per second; held in the temperature range T1 for 10 to 100 seconds to form a high-temperature-formed bainite; cooled down to a temperature range of from 200° C. to lower than 400° C. (this temperature range is hereinafter also referred to as “temperature range T2”); and held in the temperature range T2 for 200 seconds or longer. The present invention has been made based on these findings.

Initially, the metal structure that features in the second high-strength steel sheet according to the present invention will be illustrated.

Metal Structure

The second high-strength steel sheet according to the present invention has a metal structure as a mixed microstructure including polygonal ferrite, bainite, tempered martensite, and retained austenite.

Polygonal Ferrite

The second high-strength steel sheet according to the present invention has a metal structure mainly including polygonal ferrite. The term “mainly including” refers to that polygonal ferrite is present in an area percentage of greater than 50% of the entire metal structure. The polygonal ferrite microstructure is softer than bainite and functionally increases the steel sheet elongation to contribute to better workability. To exhibit these actions, the polygonal ferrite is present in an area percentage of greater than 50%, preferably 55% or more, and more preferably 60% or more, of the entire metal structure. The upper limit of the polygonal ferrite area percentage may be determined in consideration of the volume percentage (volume fraction) of the retained austenite as determined by a saturation magnetization measurement, but may for example be 85%.

Grains of the polygonal ferrite preferably have an average equivalent circle diameter D of from greater than 0 μm to 10 μm. The steel sheet can have a further higher elongation by having a small average equivalent circle diameter D of the polygonal ferrite grains and allowing the polygonal ferrite to be dispersed as smaller grains. While the detailed mechanism thereof remains unclear, this is probably because the polygonal ferrite refinement allows the polygonal ferrite to be dispersed more uniformly in the entire metal structure, this impedes nonuniform deformation and contributes to a further higher elongation. Specifically, the second high-strength steel sheet according to the present invention has a mixed metal structure including the polygonal ferrite, bainite, tempered martensite, and retained austenite. Owing to this, increasing sizes of the polygonal ferrite grains may cause variation in size of respective microstructures. Thus, nonuniform deformation may occur to cause local strain concentration, and this may probably impede improvements in workability (particularly, effective improvement in elongation due to polygonal ferrite formation). To prevent this, the polygonal ferrite grains have an average equivalent circle diameter D of preferably 10 μm or less, more preferably 8 μm or less, furthermore preferably 5 μm or less, and particularly preferably 4 μm or less.

The area percentage and average equivalent circle diameter D of the polygonal ferrite can be measured through observation with a scanning electron microscope (SEM).

Bainite and Tempered Martensite

A feature of the second high-strength steel sheet according to the present invention is that the bainite has a composite microstructure including a high-temperature-formed bainite; and a low-temperature-formed bainite having a higher strength than that of the high-temperature-formed bainite. The high-temperature-formed bainite contributes to a higher steel sheet elongation; whereas the low-temperature-formed bainite contributes to better steel sheet local formability. The steel sheet, as including the two different bainitic microstructures, can have better local formability without deterioration in elongation and exhibit better workability in general. This is probably because the combination of the bainitic microstructures differing in strength level causes nonuniform deformation and thereby increases the work hardenability.

As used herein the term “high-temperature-formed bainite” refers to a bainitic microstructure that is formed in the temperature range T1 of from 400° C. to 540° C. during a cooling process after heating to a temperature in the range of from [Ac₁ point+20° C.] to [Ac₃ point+20° C.] (two-phase temperature range). The high-temperature-formed bainite may be defined as a microstructure having an average distance of the retained austenite or the like of 1 μm or more as determined by subjecting a cross section of the steel sheet to Nital etching and observing the etched cross section with a SEM.

In contrast, the term “low-temperature-formed bainite” refers to a bainitic microstructure that is formed in the temperature range T2 of from 200° C. to lower than 400° C. during the cooling process after heating to the two-phase temperature range. The low-temperature-formed bainite may be defined as a microstructure having an average distance of the retained austenite or the like of less than 1 μm as determined by subjecting a cross section of the steel sheet to Nital etching and observing the etched cross section with a SEM.

As used herein the term “average distance of the retained austenite or the like” is defined as in the first high-strength steel sheet.

The tempered martensitic microstructure functions similarly to the low-temperature-formed bainite and contributes to better steel sheet local formability. The low-temperature-formed bainite and the tempered martensite are undistinguishable from each other even under SEM observation, and they are herein also synthetically referred to as a “low-temperature-formed bainite or the like”.

The present invention can provide a second high-strength steel sheet being improved in general workability as allowing the steel sheet to have a composite bainitic microstructure including the high-temperature-formed bainite and the low-temperature-formed bainite or the like. Specifically, the high-temperature-formed bainite is softer than the low-temperature-formed bainite or the like and contributes to a higher steel sheet elongation (EL) and better workability. In contrast, the low-temperature-formed bainite or the like is present as small grains of carbides and retained austenite, thereby relieves stress concentration upon deformation, and helps the steel sheet to have a higher stretch flangeability (λ) and/or a higher bendability (R) and to have better local formability, resulting in better workability. The second steel sheet according to the present invention includes both the high-temperature-formed bainite and the low-temperature-formed bainite or the like as a mixture, thereby has better work hardenability, and can exhibit better local formability without deterioration in elongation.

In the present invention, bainitic microstructures are classified as the “high-temperature-formed bainite” and the “the low-temperature-formed bainite or the like” by the differences in the forming temperature range and in the average distance of the retained austenite or the like. This is because the bainitic microstructures are not clearly distinguishable from each other by a general academic structural definition. Typically, lathy bainite and bainitic ferrite are classified as upper bainite and lower bainite by the transformation temperature. However, these microstructures, as well as the martensitic microstructure, are undistinguishable from one another by SEM observation in steels containing Si in a large content of 1.0% or more as in the present invention. This is because carbide precipitation associated with bainitic transformation is suppressed in such steels. According to the present invention, therefore, the bainitic microstructures are classified or distinguished not by the academic structural definition but by the differences in the forming temperature range and in the average distance of the retained austenite or the like.

The high-temperature-formed bainite and the low-temperature-formed bainite or the like may be distributed in any distribution pattern not limited. For example, both the high-temperature-formed bainite and the low-temperature-formed bainite or the like may be present in each prior austenite grain; or the high-temperature-formed bainite and the low-temperature-formed bainite or the like may be present in different prior austenite grains from each other (in this case, the high-temperature-formed bainite is present in one prior austenite grain, and the low-temperature-formed bainite or the like is present in another prior austenite grain).

How the high-temperature-formed bainite and the low-temperature-formed bainite or the like are distributed is schematically illustrated in FIG. 2.

In an embodiment, the high-temperature-formed bainite is present in an area percentage of “b” of the entire metal structure; and that the low-temperature-formed bainite or the like (the low-temperature-formed bainite and the tempered martensite) is present in a total area percentage of “c” of the entire metal structure. In this case, the area percentages “b” and “c” should each fall within the range of from 5% to 40%. Not an area percentage of the low-temperature-formed bainite, but a total area percentage of the low-temperature-formed bainite and the tempered martensite is specified herein. This is because these microstructures are undistinguishable from each other by SEM observation, as described above.

The area percentage “b” is controlled to the range of from 5% to 40%. The high-temperature-formed bainite, if present in an excessively small amount, may fail to help the steel sheet to have a sufficient elongation and to exhibit better workability. To prevent this, the area percentage “b” is 5% or more, preferably 8% or more, and more preferably 10% or more. However, the high-temperature-formed bainite, if present in an excessively large amount, may be present in an amount with poor balance with respect to the low-temperature-formed bainite or the like and fail to exhibit sufficient effects due to combination between the high-temperature-formed bainite and the low-temperature-formed bainite or the like. To prevent this, the high-temperature-formed bainite is present in an area percentage “b” of 40% or less, preferably 35% or less, more preferably 30% or less, and furthermore preferably 25% or less.

The total area percentage “c” is controlled to be from 5% to 40%. The low-temperature-formed bainite or the like, if present in an excessively small amount, may cause the steel sheet to have insufficient local formability and to fail to exhibit better workability. To prevent this, the total area percentage “c” is 5% or more, preferably 8% or more, and more preferably 10% or more. However, the low-temperature-formed bainite or the like, if present in an excessively large amount, may have poor balance in amount with respect to the high-temperature-formed bainite and fail to exhibit sufficient effects of the combination with the high-temperature-formed bainite. To prevent this, the low-temperature-formed bainite or the like is present in an area percentage “c” of 40% or less, preferably 35% or less, more preferably 30% or less, and furthermore preferably 25% or less.

The area percentage “b” and the total area percentage “c” may be in any relationship with each other, as long as they fall within the above-specified ranges respectively. All embodiments where “b” is larger than “c”; where “b” is smaller than “c”; and where “b” equals “c” are included herein.

The ratio between the high-temperature-formed bainite and the low-temperature-formed bainite or the like may be determined according to properties required of the steel sheet. Specifically, to further improve the local formability (particularly, stretch flangeability (λ)) among the steel sheet workability, the ratio of the high-temperature-formed bainite may be minimized, whereas the ratio of the low-temperature-formed bainite or the like may be maximized. To further improve the elongation among the steel sheet workability, the ratio of the high-temperature-formed bainite may be maximized, whereas the ratio of he low-temperature-formed bainite or the like may be minimized. To further increase the steel sheet strength, the ratio of the low-temperature-formed bainite or the like may be maximized, whereas the ratio of the high-temperature-formed bainite may be minimized.

The term “bainite” herein also includes bainitic ferrite. The bainite is a microstructure where a carbide is precipitated; whereas the bainitic ferrite is a microstructure where no carbide is precipitated.

Polygonal Ferrite, Bainite, and Tempered Martensite

In a preferred embodiment of the present invention, the total (a+b+c) of the area percentages “a”, “b”, and “c” is 70% or more of the entire metal structure. The area percentage “a” is an area percentage of the polygonal ferrite. The area percentage “b” is an area percentage of the high-temperature-formed bainite. The area percentage “c” is a total area percentage of the low-temperature-formed bainite or the like (the low-temperature-formed bainite and tempered martensite). The steel sheet, if having a total area percentage (a+b+c) of less than 70%, may have an insufficient elongation. The total area percentage (a+b+c) is more preferably 75% or more, and furthermore preferably 80% or more. The upper limit of the total area percentage (a+b+c) may be decided in consideration of the volume percentage of the retained austenite as determined by a saturation magnetization measurement, but may for example be 95%.

Retained Austenite

The retained austenite is specified herein as in the first high-strength steel sheet, and the explanation thereof is omitted.

Others

The second high-strength steel sheet according to the present invention has a metal structure including polygonal ferrite, bainite, tempered martensite, and retained austenite as described above. The metal structure may include these microstructures exclusively, but may further include any of other microstructures within ranges not adversely affecting advantageous effects of the present invention. The other microstructures are exemplified by (a) a martensite-austenite constituent including both as-quenched martensite and retained austenite in combination; and (b) pearlite.

The (a) martensite-austenite constituents and (b) pearlite are specified as in the first high-strength steel sheet, and the explanation thereof is omitted.

The measurement procedure of the metal structure is as with the procedure illustrated in the first high-strength steel sheet, and the explanation thereof is omitted.

Next, a chemical composition of the second high-strength steel sheet according to the present invention will be illustrated.

Chemical Composition

The second high-strength steel sheet according to the present invention satisfactorily contains C in a content of from 0.10% to 0.3%; Si in a content of from 1.0% to 3%; Mn in a content of from 1.0% to 2.5%; and Al in a content of from 0.005% to 3% and is controlled to contain Pin a content of from greater than 0% to 0.1%; and S in a content of from greater than 0% to 0.05%. Reasons for specifying these ranges are as in the first high-strength steel sheet, except for Si and Mn. Hereinafter the reasons for specifying the Si and Mn contents alone will be described.

Silicon (Si) element serves as a solute strengthening element and very importantly contributes to a higher strength of the steel sheet, suppresses carbide precipitation during the holding in the temperature range T1 and the temperature range T2 (during the austemper process), and allows effective formation of the retained austenite. To exhibit these actions, the Si content is controlled to 1.0% or more, preferably 1.2% or more, and more preferably 1.3% or more. However, Si, if contained in excess, may impede reverse transformation to the austenite phase during heating/soaking in annealing, thereby cause a large amount of the polygonal ferrite to remain, and cause the steel sheet to have an insufficient strength. Such excessive Si may form silicon scales on the steel sheet surface upon hot rolling and cause the steel sheet to have poor surface quality. To prevent these, the Si content is controlled to 3% or less, preferably 2.50% or less, and more preferably 2.0% or less.

Manganese (Mn) element is necessary for obtaining the bainite and tempered martensite and effectively stabilizes austenite to form the retained austenite. To exhibit these actions, the Mn content is controlled to 1.0% or more, preferably 1.5% or more, and more preferably 1.8% or more. However, Mn, if contained in excess, may significantly impede the formation of the high-temperature-formed bainite and invite deterioration in weldability and in workability due to segregation. To prevent this, the Mn content is controlled to 2.5% or less, preferably 2.4% or less, and more preferably 2.3% or less.

As with the first high-strength steel sheet, the second high-strength steel sheet according to the present invention may further contain at least one element selected typically from:

(a) Cr in a content of from greater than 0% to 1% and/or Mo in a content of from greater than 0% to 1%;

(b) at least one element selected from the group consisting of Ti in a content of from greater than 0% to 0.15%, Nb in a content of from greater than 0% to 0.15%, and V in a content of from greater than 0% to 0.15%;

(c) Cu in a content of from greater than 0% to 1% and/or Ni in a content of from greater than 0% to 1%;

(d) B in a content of from greater than 0% to 0.005%;

(e) at least one element selected from the group consisting of Ca in a content of from greater than 0% to 0.01%, Mg in a content of from greater than 0% to 0.01%, and a rare-earth element in a content of from greater than 0% to 0.01%. Reasons for specifying these ranges are as in the first high-strength steel sheet, and the explanation thereof is omitted here.

The second high-strength steel sheet according to the present invention has a tensile strength of 590 MPa or more and exhibits superior workability because of having a satisfactory elongation and good local formability. The second high-strength steel sheet is advantageously usable as materials for automotive structural parts, as with the first high-strength steel sheet.

The second high-strength steel sheet also has good warm workability and is advantageously usable as materials in warm forming. As used herein the term “warm working” (warm forming) refers to forming in a temperature range of from about 50° C. to about 500° C.

The metal structure and the chemical composition of the second high-strength steel sheet according to the present invention have been described above.

Next, a method capable of manufacturing the second high-strength steel sheet will be illustrated. The second high-strength steel sheet can be manufactured by a method including the steps of heating a steel sheet to a temperature range of from [Ac₁ point+20° C.] to [Ac₃ point+20° C.] (two-phase temperature range), the steel sheet having a chemical composition within the above-specified ranges; holding the steel sheet in the temperature range for 50 seconds or longer; cooling the steel sheet down to an arbitrary temperature T at an average cooling rate of from 2° C. to 50° C. per second, the temperature T falling within a range specified by Expression (1); holding the steel sheet in the temperature range specified by Expression (1) for 10 to 100 seconds; and holding the steel sheet in a temperature range specified by Expression (2) for 200 seconds or longer, in this order. The respective steps will be illustrated in order below. Expressions (1) and (2) are expressed as follows:

400° C.≦T1(° C.)≦540° C.  (1)

200° C.≦T2(° C.)<400° C.  (2)

Initially, a high-strength steel sheet is prepared by hot-rolling a slab according to a common procedure to give a hot-rolled steel sheet; and cold-rolling the hot-rolled steel sheet. This is prepared as a high-strength steel sheet to be heated to the two-phase temperature range [temperature range of from [Ac₁ point+20° C.] to [Ac₃ point+20° C.]]. The hot rolling may be performed at a finishing mill delivery temperature of typically 800° C. or higher and a coiling temperature of typically 700° C. or lower. The cold rolling may be performed to a cold rolling reduction in the range of typically from 10% to 70%.

The cold-rolled steel sheet obtained after cold rolling is heated to the temperature range of from [Ac₁ point+20° C.] to [Ac₃ point+20° C.] and held within the temperature range for 50 seconds or longer for soaking in a continuous annealing line.

The heating to a temperature falling within the ferrite-austenite two-phase temperature range allows the formation of polygonal ferrite in a predetermined amount. Specifically, heating to an excessively high temperature may cause the steel sheet to have a temperature falling within the austenite single-phase range, thereby suppress the formation of polygonal ferrite, and cause the steel sheet to fail to have a higher elongation and better workability. To prevent this, the heating temperature is controlled to [Ac₃ point+20° C.] or lower, preferably [Ac₃ point+10° C.] or lower, and more preferably lower than the Ac₃ point. The steel sheet, when heated to a temperature equal to or higher than the Ac₃ point, has a temperature falling within the austenite single-phase temperature range. However, when heating is performed to a temperature of equal to or lower than [Ac₃ point+20° C.], a small amount of polygonal ferrite can remain even after soaking (holding) for a duration on the order of the soaking time as specified in the present invention. Thus, a predetermined amount of polygonal ferrite can be formed by regulating the average cooling rate after soaking as mentioned later. In contrast, heating, if performed to a temperature of lower than [Ac₁ point+20° C.], may cause the excessive formation of polygonal ferrite. This may cause the steel sheet to fail to contain predetermined amounts of the high-temperature-formed bainite, the low-temperature-formed bainite or the like, and the retained austenite, resulting in insufficient workability. To prevent this, the heating temperature is controlled to [Ac₁ point+20° C.] or higher, preferably [Ac₁ point+30° C.] or higher, and more preferably [Ac₁ point+50° C.] or higher.

Soaking in the two-phase temperature range, if performed for a time of shorter than 50 seconds, may fail to heat the steel sheet uniformly, and this may impede the formation of the retained austenite and cause the steel sheet to have an elongation and local formability at insufficient levels and to exhibit unsatisfactory workability. To prevent this, the soaking time is controlled to 50 seconds or longer and preferably 100 seconds or longer. However, soaking, if performed for an excessively long time, may cause the austenite grains to have larger sizes, sequentially cause the polygonal ferrite grains to have larger sizes, and readily cause the steel sheet to have elongation and local formability at insufficient levels. To prevent this, the soaking time is preferably 500 seconds or shorter and more preferably 450 seconds or shorter.

The heating of the cold-rolled steel sheet to the two-phase temperature range may be performed at an average heating rate of typically 1° C. or above per second.

The Ac₁ point and the Acs point can be calculated from Expressions (a) and (b), which are described in “Leslie Tekko Zairyo Kagaku (in Japanese; translation of “The Physical Metallurgy of Steels” by Leslie)”, Maruzen Co., Ltd., May 31, 1985, p. 273, as in the first high-strength steel sheet.

After being heated to the two-phase temperature range and held in the range for 50 seconds or longer for soaking, the steel sheet is cooled down to an arbitrary temperature T at an average cooling rate of from 2° C. to 50° C. per second. The temperature T falls within the range specified by Expression (1). Thus, the steel sheet is cooled at a predetermined average cooling rate or higher in a temperature range of from the two-phase temperature range down to the arbitrary temperature T falling within the range specified by Expression (1). This allows the formation of a predetermined amount of polygonal ferrite and the formation of both the high-temperature-formed bainite and the low-temperature-formed bainite or the like. Cooling in this temperature range, if performed at an average cooling rate of lower than 2° C. per second, may cause pearlite transformation to form pearlite in excess, and this may cause the steel sheet to have an insufficient elongation and to exhibit unsatisfactory workability. The average cooling rate in this temperature range is preferably 5° C. or above per second, and more preferably 10° C. or above per second. However, cooling in the temperature range, if performed at an excessively high average cooling rate, may impede the formation of a predetermined amount of polygonal ferrite. To prevent this, the average cooling rate is controlled to 50° C. or below per second, preferably 40° C. or below per second, and more preferably 30° C. or below per second.

After being cooled down to the arbitrary temperature T falling within the range specified by Expression (1), the steel sheet is held in the temperature range T1 specified by Expression (1) for 10 to 100 seconds; and then held in the temperature range T2 specified by Expression (2) for 200 seconds or longer. Suitable separate controls of the holding times in the temperature range T1 and in the temperature range T2 allow the formation of predetermined amounts of the high-temperature-formed bainite and the low-temperature-formed bainite or the like, respectively.

Specific conditions for holding in the temperature range T1 and in the temperature range T2 are as with the conditions described in the first high-strength steel sheet, and the description thereof is omitted here.

After being held in the temperature range T2 for a predetermined time, the steel sheet is cooled down to room temperature and yields a second high-strength steel sheet according to the present invention.

The first high-strength steel sheet may bear a hot-dip galvanized layer or a hot-dip galvannealed layer on a surface thereof, as with the first high-strength steel sheet.

The hot-dip galvanized layer or the hot-dip galvannealed layer may be formed under any conditions not limited, such as known conditions. Specific conditions are as in the first high-strength steel sheet, and the description thereof is omitted here.

The technique according to the present invention is advantageously applicable particularly to thin steel sheets having a thickness of 3 mm or less.

The second high-strength steel sheet according to the present invention has been described above.

The present application is based on Japanese Patent Application No. 2011-080953 filed on Mar. 31, 2011; Japanese Patent Application No. 2011-080954 filed on Mar. 31, 2011; Japanese Patent Application No. 2011-197670 filed on Sep. 9, 2011; and Japanese Patent Application No. 2011-197671 filed on Sep. 9, 2011, the entire contents of which are incorporated herein by reference.

EXAMPLES

The present invention will be illustrated in further detail with reference to several experimental examples below. It should be noted, however, that the examples are by no means construed to limit the scope of the invention; and various changes and modifications without departing from the spirit and scope of the invention are possible and fall within the scope of the invention. Following Experimental Example 1 is an experimental example relating to the first high-strength steel sheet; and Experimental Example 2 is an experimental example relating to the second high-strength steel sheet.

Experimental Example 1

Experimental slabs were prepared by subjecting steels having chemical compositions given in Tables 1 and 2 below (with the remainder consisting of iron and inevitable impurities other than P, S, N, and O) to vacuum ingot making. The rare-earth elements (REM) in Tables 1 and 2 employed a misch metal containing about 50% of La and about 30% of Ce.

The Ac₁ points and the Ac₃ points of the steels (slabs) were calculated based on the chemical compositions given in Tables 1 and 2 and on Expression (a) and Expression (b), respectively. The results are indicated in Tables 3 to 5 below.

The prepared experimental slabs were sequentially subjected to hot rolling, cold rolling, and continuous annealing and yielded specimens. Specific conditions are as follows.

The experimental slabs were heated to 1250° C. and held at this temperature for 30 minutes, hot-rolled to a rolling reduction of about 90% at a finishing mill delivery temperature of 920° C., and cooled from this temperature down to a coiling temperature of 500° C. at an average cooling rate of 30° C., and coiled. After being coiled, the works were held at the coiling temperature (500° C.) for 30 minutes, then cooled down to room temperature through furnace cooling, and yielded hot-rolled steel sheets having a thickness of 2.6 mm.

The resulting hot-rolled steel sheets were subjected to acid wash to remove surface scales, cold-rolled to a cold rolling reduction of 46%, and yielded cold-rolled steel sheets having a thickness of 1.4 mm.

The resulting cold-rolled steel sheets were heated to temperatures (° C.) given in Tables 3 to 5, held for durations given in Tables 3 to 5 for soaking, cooled according to any of the following four patterns, subjected to continuous annealing, and yielded the specimens.

Cooling Pattern i: corresponding to the pattern (i) in FIG. 3

After the soaking, a work was cooled down to a start temperature T (° C.) given in Tables 3 to 5 at an average cooling rate (° C. per second) given in Tables 3 to 5, held at this start temperature T (° C.), then cooled down to a start temperature (° C.) in the temperature range T2 given in Tables 3 to 5, and held at this start temperature. Tables 3 to 5 indicate a residence time (second) in the temperature range T1; and a residence time (second) in the temperature range T2. The tables also indicate a time (second) from the time point at which holding in the temperature range T1 was completed to the time point at which the work temperature reached the start temperature in the temperature range T2.

Cooling Pattern ii: corresponding to the pattern (ii) in FIG. 3

After the soaking, a work was cooled down to a start temperature T (° C.) given in Tables 3 to 5 at an average cooling rate (° C. per second) given in Tables 3 to 5, subsequently cooled down to an end temperature (° C.) given in Tables 3 to 5, cooled down to a start temperature (° C.) in the temperature range T2 given in Tables 3 to 5, and held at this start temperature for a duration (second) given in Tables 3 to 5. Tables 3 to 5 indicate a residence time (second) in the temperature range T1; and a residence time (second) in the temperature range T2. The tables also indicate a time (second) from the time point at which holding in the temperature range T1 was completed to the time point at which the work temperature reached the start temperature in the temperature range T2.

Cooling Pattern iii; corresponding to the pattern (iii) in FIG. 3

After the soaking, a work was cooled down to a start temperature T (° C.) given in Tables 3 and 4 at an average cooling rate (° C. per second) given in Tables 3 and 4, then cooled down to a start temperature (° C.) in the temperature range T2 given in Tables 3 and 4, and held at this start temperature. Tables 3 and 4 indicate a residence time (second) in the temperature range T1; and a residence time (second) in the temperature range T2.

Cooling Pattern iv

After the soaking, a work was cooled down to a start temperature (° C.) in the temperature range T1 or to a start temperature (° C.) in the temperature range T2, each as given in Table 3, and held at the start temperature in question. Specifically, Sample No. 8 in Table 3 was a sample, in which the work after the soaking was held at 420° C. for 450 seconds and then cooled down to room temperature at an average cooling rate of 5° C. per second without holding (without stopping). The residence time in the temperature range T2 of this sample indicated in Table 3 refers to a time necessary to pass through the temperature range T2. Sample No. 15 in Table 3 was a sample, in which the work after the soaking was held at 380° C. for 450 seconds and then cooled down to room temperature at an average cooling rate of 5° C. per second without holding (without stopping). The residence time in the temperature range T1 of this sample indicated in Table 3 refers to a time necessary to pass through the temperature range T1. Table 3 also indicates a residence time in the temperature range T1 (second) and a residence time in the temperature range T2 (second).

Of the start temperatures and the end temperatures in the temperature range T1; and of the start temperatures in the temperature range T2 given in Tables 3 to 5, each of the asterisked values was out of the temperature range T1 or the temperature range T2 as specified in the present invention, but was indicated as a temperature in each column for convenience of explanation of the heat pattern.

The prepared specimens were subjected to metal structure observation and mechanical properties evaluation according to the following procedures.

Metal Structure Observation

Of the metal structure, area percentages of the high-temperature-formed bainite, the low-temperature-formed bainite or the like (namely, the low-temperature-formed bainite and the tempered martensite), and the polygonal ferrite were calculated based on an observation with a scanning electron microscope (SEM); whereas a volume percentage of the retained austenite was determined by a saturation magnetization measurement.

(1) Area Percentages of High-Temperature-Formed Bainite, Low-Temperature-Formed Bainite and the Like, and Polygonal Ferrite

To determine these area percentages, a specimen cross section parallel to the rolling direction was surface-polished, further electropolished, etched with a Nital solution, and a position at a one-fourth depth the sheet thickness was observed in five view fields with a SEM at a 3000-fold magnification. One view field to be observed had a size of about 50 μm long by about 50 μm wide.

Next, average distances of retained austenite and carbide observed as white or pale gray microstructures in the observation view fields were measured according to the method mentioned above. a high-temperature-formed bainite and a low-temperature-formed bainite or the like were distinguished from each other by the average distance, whose area percentages were measured by point counting.

Tables 6 to 8 indicate an area percentage “a” (%) of the high-temperature-formed bainite, a total area percentage “b” (%) of the low-temperature-formed bainite and tempered martensite, and an area percentage “c” (%) of the polygonal ferrite. The tables also indicate a total area percentage (a+b+c) of the area percentage “a”, the total area percentage “b”, and the area percentage “c”.

Equivalent circle diameters of polygonal ferrite grains observed in the observation view fields were measured and averaged. The results are indicated in Tables 6 to 8. In addition, a sample having an average equivalent circle diameter D of polygonal ferrite grains of 10 μm or less was evaluated as “∘” (good), and one having an average equivalent circle diameter of greater than 10 μm was evaluated as “Δ” (fair). The evaluation results are indicated in Tables 6 to 8.

(2) Retained Austenite Volume Percentage

Of the metal structure, a volume percentage of the retained austenite was determined by a saturation magnetization measurement. Specifically, a saturation magnetization (I) of a specimen and a saturation magnetization (Is) of a standard specimen were measured, based on which a volume percentage (Vγr) of the retained austenite was determined according to an expression below. The standard specimen had been subjected to a heat treatment at 400° C. for 15 hours. The saturation magnetization measurement was performed at room temperature with a DC magnetization B-H curve automatic recorder “Model BHS-40” supplied by Riken Denshi Co., Ltd. with a maximum applied magnetization of 5000 (Oe). The expression is expressed as follows:

Vγr=(1−I/Is)×100

Equivalent circle diameters “d” of martensite-austenite constituents including both retained austenite and as-quenched martensite in combination were measured by polishing a surface of a specimen cross section parallel to the rolling direction, and observing the polished surface in five view fields with an optical microscope at a 1000-fold magnification. A number percentage of martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm with respect to the total number of the entire martensite-austenite constituents in the observed cross-section was calculated. A specimen having a number percentage of less than 15% was evaluated as accepted (∘), whereas a specimen having a number percentage of 15% or more was evaluated as rejected (x). The evaluation results are indicated in Tables 6 to 8.

Mechanical Properties Evaluation

Mechanical properties of each specimen were evaluated based on the tensile strength (TS), elongation (EL), bore expansion ratio (A), critical bending radius (R), and Erichsen value.

(1) The tensile strength (TS) and elongation (EL) were measured through a tensile test according to Japanese Industrial Standard (JIS) Z2241. As a test specimen, a JIS Z 2201 No. 5 test specimen was cut from the specimen so that a direction perpendicular to the specimen rolling direction be a longitudinal direction of the test specimen. The measurement results are indicated in Tables 6 to 8.

(2) Stretch flangeability was evaluated based on the bore expansion ratio. The bore expansion ratio (λ) was measured through a bore expanding test according to the Japan Iron and Steel Federation Standard (JFS) T 1001. The measurement results are indicated in Tables 6 to 8.

(3) The critical bending radius (R) was measured through a V-bending test according to JIS Z 2248. As a test specimen, a JIS Z 2204 No. 1 test specimen (thickness: 1.4 mm) was cut from the specimen so that a direction perpendicular to the specimen rolling direction be a longitudinal direction of the test specimen (i.e., so that the bend line agree with the rolling direction). The V-bending test was performed after applying mechanical grinding to a longitudinal end face of the test specimen so as to prevent cracking.

The V-bending test was performed at an angle between a die and a punch of 90° and at a punch tip radius varying in units of 0.5 mm. A minimum punch tip radius at which the test specimen can be bent without cracking was determined as the critical bending radius (R). The measurement results are indicated in Tables 6 to 8. The presence/absence of cracking was observed with a magnifying glass, and a test specimen without the occurrence of hair crack was evaluated as suffering from no cracking.

(4) The Erichsen value was measured through an Erichsen test according to JIS Z 2247. A test specimen of a size of 90 mm long by 90 mm wide by 1.4 mm thick was prepared by cutting from the specimen. The Erichsen test was performed with a device having a punch diameter of 20 mm. The measurement results are indicated in Tables 6 to 8. The Erichsen test enables evaluations of both the total elongation properties and the local ductility of the steel sheet.

The mechanical properties of the specimen were evaluated based on criteria for the elongation (EL), bore expansion ratio (λ), critical bending radius (R), and Erichsen value varying depending on the tensile strength (TS). Specifically, required properties including EL, λ, R, and Erichsen value vary depending on the steel sheet tensile strength TS. Accordingly, the mechanical properties were evaluated in accordance with the following criteria that vary depending on the TS level.

Based on the criteria, a sample evaluated as satisfactory all in the properties of EL, λ, R, and Erichsen value were evaluated as accepted (∘), whereas one evaluated as not satisfying the criteria in one or more of the properties was evaluated as rejected (x). The evaluation results are indicated in Tables 6 to 8.

-   -   (1) TS of 780 MPa grade

TS: from 780 MPa to less than 980 MPa

EL: 25% or more

λ: 30% or more

R: 1.0 mm or less

Erichsen value: 10.4 mm or more

-   -   (2) TS of 980 MPa grade

TS: from 980 MPa to less than 1180 MPa

EL: 19% or more

λ: 20% or more

R: 3.0 mm or less

Erichsen value: 10.0 mm or more

-   -   (3) TS of 1180 MPa grade

TS: from 1180 MPa to less than 1270 MPa

EL: 15% or more

λ: 20% or more

R: 4.5 mm or less

Erichsen value: 9.6 mm or more

-   -   (4) TS of 1270 MPa grade

TS: from 1270 MPa to less than 1370 MPa

EL: 14% or more

λ: 20% or more

R: 5.5 mm or less

Erichsen value: 9.4 mm or more

The first high-strength steel sheet is designed to be applied to steel sheets having a tensile strength TS of from 780 MPa to less than 1370 MPa. Samples having a tensile strength TS of less than 780 MPa, or of 1370 MPa or more were ineligible herein even when being satisfactory in EL, λ, R, and Erichsen value.

Tables 1 to 8 demonstrate as follows. Of Samples Nos. 1 to 70 indicated in Tables 6 to 8, Samples Nos. 4, 29, 31, 38, 55, 65, and 67 underwent cooling in Pattern i; Samples Nos. 7, 11, 14, and 33 underwent cooling in Pattern Samples Nos. 8 and 15 underwent cooling in Pattern iv; and the other samples underwent cooling in Pattern

Samples evaluated as “∘” in the assessment (general evaluation) in Tables 6 to 8 were steel sheets satisfying the conditions specified in the present invention and satisfying criteria values of the mechanical properties (EL, λ, R, and Erichsen value) determined according to the tensile strength TS. This demonstrates that high-strength steel sheets according to the present invention exhibited good workability in general.

By contrast, samples evaluated as “x” in the assessment (Samples Nos. 8, 13, 15, 29, 31, 34, 37, 41, 46, 48, 52, and 60 to 63 in Tables 6 to 8) were steel sheets not satisfying one or more of the conditions specified in the present invention. Details thereof are as follows.

Sample No. 8 in Table 6 underwent holding in the temperature range T1 for an excessively long time and subsequent cooling without holding in the temperature range T2. This sample suffered from insufficient formation of the low-temperature-formed bainite or the like and heavy formation of coarse martensite-austenite constituents. The sample thereby had a low bore expansion ratio X and failed to exhibit better workability. Sample No. 13 in Table 6 underwent, after being heated to and held in the two-phase temperature range, cooling down to an arbitrary temperature T falling within the range specified by Expression (1) at an excessively low average cooling rate. This sample suffered from pearlite transformation, failed to include a sufficient amount of retained austenite, had an insufficient elongation, and failed to exhibit better workability. Sample No. 15 in Table 6 underwent cooling down to the temperature range T2 after soaking without holding in the temperature range T1 (without stopping), and holding in the temperature range T2. This sample suffered from little formation of the high-temperature-formed bainite because of being held only in the temperature range T2, had a low elongation and poor local formability (Erichsen value), and failed to exhibit better workability. Sample No. 29 in Table 6 underwent, after soaking, cooling down to the temperature range T2 without holding in the temperature range T1 (without stopping), and holding at two different temperatures in the temperature range T2. This sample suffered from little formation of the high-temperature-formed bainite because of being held only in the temperature range T2, had a low elongation, and failed to exhibit better workability.

Sample No. 31 in Table 6 underwent holding in the temperature range T1 for an excessively short time. This sample suffered from formation of an excessively small amount of the high-temperature-formed bainite, thereby had a low elongation, and failed to exhibit better workability. Sample No. 34 in Table 7 underwent holding in the temperature range T1 for an excessively long time without holding in the temperature range T2. This sample suffered from insufficient formation of the low-temperature-formed bainite or the like and heavy formation of coarse martensite-austenite constituents. The sample thereby had a low Erichsen value and poor local formability and failed to exhibit better workability. Sample No. 37 in Table 7 underwent heating at an excessively high temperature. This sample suffered from no formation of polygonal ferrite, had a low elongation, and failed to exhibit better steel sheet workability. Sample No. 41 in Table 7 underwent heating at an excessively low temperature, suffered from excessive formation of polygonal ferrite, and had an insufficient strength.

Sample No. 46 in Table 7 underwent holding in the two-phase temperature range for an excessively short time and suffered from insufficient formation of the retained austenite. This sample had a low elongation and a low Erichsen value to exhibit poor local formability, and failed to exhibit better steel sheet workability. Sample No. 48 in Table 7 underwent, after soaking, holding at a temperature higher than the temperature range T1 specified in the present invention, subsequently cooling down to the temperature range T2 without holding in the temperature range T1, and holding in the temperature range T2. This sample suffered from excessive formation of polygonal ferrite, insufficient formation of the high-temperature-formed bainite, thereby had a low elongation, and failed to exhibit better workability. Sample No. 52 in Table 7 underwent, after holding in the temperature range T1, cooling down to a temperature lower than the temperature range T2 without holding in the temperature range T2. This sample suffered from little formation of the low-temperature-formed bainite, included a large amount of coarse martensite-austenite constituents as identified through SEM observation, and include a large amount of as-quenched martensite. The sample thereby had an excessively high strength.

Sample No. 60 in Table 8 had an excessively low carbon content. This sample suffered from formation of an excessively small amount of the retained austenite, had a low elongation and a low Erichsen value, and failed to exhibit better workability. Sample No. 61 in Table 8 had an excessively high Si content. This sample suffered from excessive formation of polygonal ferrite, suffered from insufficient formation of the high-temperature-formed bainite and the low-temperature-formed bainite or the like, and failed to have a strength surely at a desired level. Sample No. 62 in Table 8 had an excessively low Si content. This sample suffered from insufficient formation of the retained austenite, thereby had a low elongation, and failed to exhibit better workability. Sample No. 63 in Table 8 had an excessively low Mn content and underwent insufficient quenching. This sample suffered from excessive formation of polygonal ferrite, but insufficient formation of the low-temperature-formed bainite or the like during cooling. The sample had a low elongation, a small bore expansion ratio, and a low Erichsen value, and failed to exhibit better workability.

These results demonstrate that the present invention can provide high-strength steel sheets having better workability.

Steel sheets having a tensile strength of 980 MPa grade are indicated in Tables 6 and 7. Among them, Samples Nos. 3 to 7, 9 to 12, 14, 16 to 27, 30, 32, 33, 35, 36, 38 to 40, and 42 satisfied the conditions specified in the present invention. Relating to these samples, a relationship between the elongation (EL) and the tensile strength (TS) is illustrated in FIG. 4. In FIG. 4, data indicated by the symbol “” (filled circle) are data of samples having an average equivalent circle diameter D of polygonal ferrite grains of 10 μm or less; and data indicated by the symbol “▪” (filled square) are data of samples having an average equivalent circle diameter D of polygonal ferrite grains of greater than 10 μm.

FIG. 4 demonstrates that steel sheets could have a higher elongation (EL) and exhibit further better workability by controlling the average equivalent circle diameter D of polygonal ferrite grains to 10 μm or less, even when having a tensile strength (TS) at an equivalent level.

TABLE 1 Steel Chemical composition (in mass percent) type C Si Mn P S Al Cr Mo Ti Nb V Cu Ni B Ca Mg REM N O a 0.17 1.41 1.80 0.02 0.002 0.03 — — — — — — — — — — — 0.002 0.001 b 0.13 1.85 1.65 0.02 0.002 0.04 — — — — — — — — — — — 0.003 0.001 c 0.17 1.78 2.28 0.03 0.002 0.04 — — — — — — — — — — — 0.004 0.001 d 0.17 2.18 2.31 0.03 0.001 0.05 — — — — — — — — — — — 0.004 0.001 e 0.17 1.85 1.89 0.03 0.002 0.03 0.3 — — — — — — — — — — 0.004 0.001 f 0.17 1.82 2.09 0.02 0.001 0.04 — 0.2 — — — — — — — — — 0.003 0.001 g 0.17 2.02 2.22 0.02 0.002 0.04 — — 0.08 — — — — — — — — 0.005 0.001 h 0.17 1.98 2.21 0.01 0.002 0.03 — — 0.03 0.04 — — — — — — — 0.003 0.001 i 0.16 2.01 2.26 0.03 0.002 0.05 — — 0.03 — 0.06 — — — — — — 0.004 0.001 j 0.17 1.82 2.01 0.01 0.001 0.03 — — — — — 0.34 0.38 — — — — 0.002 0.002 k 0.18 1.77 1.95 0.01 0.002 0.05 — — 0.02 — — — — 0.0022 — — — 0.004 0.001 l 0.15 1.95 2.34 0.02 0.002 0.03 — — — — — — — — 0.0025 0.0013 0.0015 0.004 0.001 m 0.17 2.02 2.05 0.01 0.002 0.03 — — — — — — — — 0.0035 — 0.0022 0.002 0.001 n 0.24 1.75 2.25 0.02 0.001 0.02 — — — — — — — — — — — 0.002 0.001 o 0.16 1.35 2.19 0.02 0.001 0.03 — — — — — — — 0.0005 — — — 0.003 0.001 p 0.13 2.15 2.50 0.01 0.002 0.03 — — — — — — — — — — — 0.003 0.001 q 0.28 1.15 1.80 0.01 0.002 0.33 — — — — — — — — — — — 0.003 0.001 r 0.12 2.78 2.54 0.02 0.001 0.04 — — — — — — — — — — — 0.004 0.001 s 0.17 1.38 1.67 0.03 0.001 0.04 0.5 0.2 — — — — — — — — — 0.003 0.001 t 0.23 2.31 2.26 0.02 0.002 0.05 — — — — — — — — — — — 0.003 0.001 u 0.25 1.76 2.47 0.02 0.001 0.04 — — — — — — — — — — — 0.003 0.001 v 0.19 2.01 2.63 0.01 0.001 0.03 — — 0.02 — — — — — — — — 0.003 0.001 w 0.28 1.55 2.33 0.01 0.002 0.03 — — — — — — — — — — — 0.003 0.001 x 0.17 2.65 2.85 0.02 0.002 0.04 — — — — — — — — — — — 0.003 0.001 y 0.29 1.12 2.73 0.01 0.002 1.02 — — — — — — — — — — — 0.003 0.001 z 0.19 2.02 2.59 0.03 0.001 0.04 0.6 — 0.07 — — 0.12 0.11 — — — — 0.002 0.001

TABLE 2 Steel Chemical composition (in mass percent) type C Si Mn P S Al Cr Mo Ti Nb V Cu Ni B Ca Mg REM N O α 0.23 2.31 2.43 0.02 0.002 0.03 — 0.3 0.02 — — — — 0.0025 0.0022 — 0.0021 0.002 0.002 β 0.08 1.88 2.24 0.02 0.001 0.04 — — — — — — — — — — — 0.003 0.001 γ 0.15 3.22 2.18 0.02 0.002 0.04 — — — — — — — — — — — 0.004 0.001 δ 0.17 0.45 2.27 0.01 0.001 0.04 — — — — — — — — — — — 0.004 0.001 ε 0.17 1.81 1.27 0.02 0.002 0.02 — — — — — — — — — — — 0.003 0.001 ζ 0.19 1.99 2.17 0.02 0.001 0.02 — — — 0.05 — — — — — — — 0.004 0.001 η 0.19 2.03 2.23 0.01 0.002 0.03 — — — — 0.11 — — — — — — 0.003 0.001 ι 0.19 1.97 2.20 0.02 0.002 0.04 — — — — — 0.05 — — — — — 0.004 0.001 κ 0.19 1.98 2.21 0.02 0.002 0.03 — — — — — — 0.56 — — — — 0.002 0.001 λ 0.18 2.01 2.22 0.03 0.001 0.04 — — — — — — — — 0.0015 — — 0.005 0.001 μ 0.19 1.99 2.20 0.03 0.002 0.05 — — — — — — — — — 0.0020 — 0.005 0.001 ν 0.18 2.02 2.18 0.01 0.003 0.03 — — — — — — — — — — 0.0023 0.002 0.001

TABLE 3 Soaking [(Ac₁ + Heating Holding Average Steel Ac₁ Ac₃ Ac₃)/2] + 20 Ac₃ + 20 temperature time cooling rate No. type (° C.) (° C.) (° C.) (° C.) (° C.) (sec) (° C./sec) 1 a 745 861 823 881 850 70 60 2 b 759 900 850 920 890 200 60 3 c 750 874 832 894 870 200 30 4 c 750 874 832 894 870 200 80 5 c 750 874 832 894 870 200 30 6 c 750 874 832 894 870 200 30 7 c 750 874 832 894 870 200 30 8 c 750 874 832 894 870 200 30 9 d 762 895 849 915 880 200 30 10 d 762 895 849 915 890 480 15 11 d 762 895 849 915 880 200 30 12 d 762 895 849 915 880 200 10 13 d 762 895 849 915 880 200 1 14 d 762 895 849 915 880 200 30 15 d 762 895 849 915 880 200 60 16 e 762 883 842 903 880 200 95 17 f 754 882 838 902 870 450 30 18 g 758 912 855 932 900 200 30 19 h 757 876 836 896 860 200 30 20 i 757 910 854 930 900 200 30 21 j 748 854 821 874 830 200 30 22 k 754 879 837 899 870 200 30 23 l 755 874 835 894 860 200 30 24 l 755 874 835 894 860 200 10 25 l 755 874 835 894 860 200 30 26 l 755 874 835 894 860 200 30 27 l 755 874 835 894 860 200 30 28 l 755 874 835 894 870 200 30 29 l 755 874 835 894 860 200 60 30 m 760 874 837 894 860 200 90 31 m 760 874 837 894 860 200 60 Temper- Temperature ature range T1 range T2 Residence Start End Time Start time (sec) temper- temper- from T1 temper- Temper- Temper- ature T ature to T2 ature ature ature Cooling No. (° C.) (° C.) (sec) (° C.) range T1 range T2 pattern 1 450 420 4 380 29 263 ii 2 450 420 4 380 29 218 ii 3 420 400 4 350 29 484 ii 4 420 420 4 395 30 490 i 5 450 420 4 350 14 483 ii 6 450 420 20  380 93 496 ii 7 480 — — 380 30 343 iii 8 420 420 — — 458 40 iv 9 450 420 4 350 29 483 ii 10 450 420 4 350 32 483 ii 11 450 — — 380 28 496 iii 12 450 420 4 350 35 483 ii 13 450 420 4 350 116 483 ii 14 450 — — 390 86 505 iii 15 — — — 380 2 486 iv 16 450 420 4 350 42 633 ii 17 450 420 4 350 44 633 ii 18 450 420 4 350 44 633 ii 19 450 420 4 350 44 633 ii 20 450 420 4 350 44 633 ii 21 450 420 4 350 44 633 ii 22 450 420 4 350 44 633 ii 23 450 420 4 350 44 483 ii 24 480 450 4 350 33 482 ii 25 450   380  4 350 32 495 ii 26 500 480 4 320 28 476 ii 27 410 400 4 380 29 490 ii 28 420 400 4 260 19 616 ii 29   380    380  4 230 2 1835 i 30 450 420 4 350 12 283 ii 31 420 420 1 350 3 481 i

TABLE 4 Soaking [(Ac₁ + Heating Holding Average Steel Ac₁ Ac₃ Ac₃)/2] + 20 Ac₃ + 20 temperature time cooling rate No. type (° C.) (° C.) (° C.) (° C.) (° C.) (sec) (° C./sec) 32 n 750 843 817 863 830 200 30 33 n 750 843 817 863 830 200 15 34 n 750 843 817 863 830 200 30 35 o 739 849 814 869 840 200 30 36 o 739 849 814 869 840 200 30 37 o 739 849 814 869 930 200 90 38 p 759 877 838 897 870 200 15 39 q 737 939 858 959 870 200 60 40 r 777 918 867 938 910 460 30 41 r 777 918 867 938 750 200 30 42 s 754 877 835 897 870 200 15 43 t 766 882 844 902 870 200 30 44 t 766 882 844 902 870 200 30 45 t 766 882 844 902 870 200 95 46 t 766 882 844 902 850 20 30 47 u 748 843 815 863 820 200 30 48 u 748 843 815 863 820 200 30 49 v 753 857 825 877 850 200 30 50 v 753 857 825 877 850 200 5 51 v 753 857 825 877 850 200 30 52 v 753 857 825 877 850 200 30 53 w 743 817 800 837 810 200 30 54 x 770 889 849 909 880 60 30 55 x 770 889 849 909 880 200 30 56 x 770 889 849 909 880 200 3 57 y 726 1184 975 1204 990 200 30 58 z 762 889 845 909 880 200 30 Temper- Temperature ature range T1 range T2 Residence Start End Time Start time (sec) temper- temper- from T1 temper- Temper- Temper- ature T ature to T2 ature ature ature Cooling No. (° C.) (° C.) (sec) (° C.) range T1 range T2 pattern 32 450 420 4 350 84 483 ii 33 530 — — 250 22 484 iii 34 480 450 4   420  481 40 ii 35 520 490 4 350 28 481 ii 36 405 400 4 380 30 640 ii 37 450 420 4 380 28 638 ii 38 420 420 4 380 35 488 i 39 450 420 4 380 29 238 ii 40 450 420 4 350 29 483 ii 41 450 420 4 350 29 483 ii 42 450 420 4 380 53 638 ii 43 480 450 4 320 29 476 ii 44 450 420 4 230 28 610 ii 45 450 420 4 320 27 477 ii 46 450 420 4 350 29 483 ii 47 450 420 4 320 29 627 ii 48   650    620  4 380 4 636 ii 49 450 420 4 320 49 927 ii 50 450 420 4 320 64 927 ii 51 450 420 4 320 94 927 ii 52 480   250  4   150  23 43 ii 53 450 420 4 350 29 483 ii 54 480 450 4 320 64 1226 ii 55 420 420 4 320 50 1227 i 56 480 450 4 225 66 1808 ii 57 450 420 4 320 84 1827 ii 58 480 450 4 350 49 1232 ii

TABLE 5 Soaking [(Ac₁ + Heating Holding Average Steel Ac₁ Ac₃ Ac₃)/2] + 20 Ac₃ + 20 temperature time cooling rate No. type (° C.) (° C.) (° C.) (° C.) (° C.) (sec) (° C./sec) 59 α 764 886 845 906 880 200 30 60 β 754 899 847 919 890 200 30 61 γ 793 941 887 961 900 200 30 62 δ 712 801 777 821 780 200 30 63 ε 762 891 847 911 880 200 30 64 ζ 753 855 824 875 850 200 30 65 η 755 867 831 887 850 200 30 66 ι 754 864 829 884 850 200 30 67 κ 744 852 818 872 850 200 30 68 λ 755 875 835 895 860 200 30 69 μ 754 876 835 896 860 200 30 70 ν 754 856 825 876 840 200 30 Temper- Temperature ature range T1 range T2 Residence Start End Time Start time (sec) temper- temper- from T1 temper- Temper- Temper- ature T ature to T2 ature ature ature Cooling No. (° C.) (° C.) (sec) (° C.) range T1 range T2 pattern 59 480 450 4 320 64 1226 ii 60 450 420 4 380 30 638 ii 61 450 420 4 380 30 638 ii 62 450 420 4 380 30 638 ii 63 450 420 4 380 30 638 ii 64 450 420 4 320 44 927 ii 65 420 420 4 320 45 927 i 66 480   380  4 320 50 940 ii 67 450 450 4 320 45 926 i 68 450 420 4 320 44 927 ii 69 450 420 4 320 44 927 ii 70 450 420 4 320 44 927 ii

TABLE 6 Composite microstructure High-temper- Low-temper- ature-formed ature-formed Polygonal Polygonal ferrite Retained Number bainite“a” bainite“b” ferrite “c” Total area Grain austenite percentage (in area (in area (in area percentage size Evalua- (in volume of MA No. percent) percent) percent) (a + b + c) (μm) tion percent) constituent 1 22 30 38 90 3 ∘ 10 ∘ 2 18 27 45 90 4 ∘ 11 ∘ 3 18 35 33 86 5 ∘ 14 ∘ 4 27 37 15 79 4 ∘ 15 ∘ 5 14 38 34 86 5 ∘ 13 ∘ 6 34 24 29 87 5 ∘ 15 ∘ 7 22 33 31 86 4 ∘ 14 ∘ 8 47 5 33 85 4 ∘ 15 x 9 20 32 36 88 3 ∘ 14 ∘ 10 19 34 37 90 13 Δ 14 ∘ 11 18 37 35 90 4 ∘ 14 ∘ 12 13 25 47 85 4 ∘ 15 ∘ 13 0 0 67 67 5 ∘ 0 ∘ 14 27 22 34 83 4 ∘ 16 ∘ 15 3 51 37 91 4 ∘ 8 ∘ 16 35 41 14 90 5 ∘ 15 ∘ 17 23 35 27 85 12 Δ 14 ∘ 18 19 28 39 86 2 ∘ 14 ∘ 19 21 23 42 86 3 ∘ 15 ∘ 20 18 29 40 87 3 ∘ 14 ∘ 21 20 23 43 86 3 ∘ 16 ∘ 22 19 24 41 84 2 ∘ 15 ∘ 23 18 32 39 89 4 ∘ 14 ∘ 24 14 24 48 86 3 ∘ 15 ∘ 25 23 26 37 86 4 ∘ 14 ∘ 26 24 28 38 90 4 ∘ 15 ∘ 27 12 37 39 88 4 ∘ 13 ∘ 28 26 36 26 88 3 ∘ 14 ∘ 29 5 53 33 91 3 ∘ 9 ∘ 30 21 31 38 90 3 ∘ 15 ∘ 31 4 50 36 90 3 ∘ 10 ∘ TS EL λ R Erichsen No. (MPa) (%) (%) (mm) value (mm) Assessment Remarks 1 821 28 33 0.0 10.7 ∘ 780 MPa grade 2 808 29 31 0.0 10.8 ∘ 780 MPa grade 3 1012 23 28 1.5 10.4 ∘ 980 MPa grade 4 997 25 23 2.0 10.5 ∘ 980 MPa grade 5 1034 22 38 1.0 10.4 ∘ 980 MPa grade 6 1001 24 27 2.0 10.5 ∘ 980 MPa grade 7 1023 22 32 1.0 10.5 ∘ 980 MPa grade 8 1045 21 14 4.0 10.7 x 980 MPa grade 9 999 25 32 2.0 10.6 ∘ 980 MPa grade 10 983 23 27 2.5 10.3 ∘ 980 MPa grade 11 1022 23 31 1.5 10.4 ∘ 980 MPa grade 12 1001 24 27 2.0 10.5 ∘ 980 MPa grade 13 856 17 34 0.0 10.7 x 780 MPa grade 14 1035 23 28 3.0 10.5 ∘ 980 MPa grade 15 1072 17 47 3.0 9.8 x 980 MPa grade 16 986 24 47 0.0 10.6 ∘ 980 MPa grade 17 1028 21 31 0.5 10.2 ∘ 980 MPa grade 18 1046 22 28 2.0 10.4 ∘ 980 MPa grade 19 1055 21 32 1.5 10.3 ∘ 980 MPa grade 20 1027 23 30 1.5 10.4 ∘ 980 MPa grade 21 1011 24 35 1.0 10.5 ∘ 980 MPa grade 22 1012 23 27 2.0 10.4 ∘ 980 MPa grade 23 1035 23 28 1.5 10.4 ∘ 980 MPa grade 24 1027 24 26 2.0 10.5 ∘ 980 MPa grade 25 1003 25 27 1.5 10.6 ∘ 980 MPa grade 26 992 25 28 1.5 10.6 ∘ 980 MPa grade 27 1024 22 38 0.5 10.4 ∘ 980 MPa grade 28 1203 18 32 3.5 10.1 ∘ 1180 MPa grade  29 1199 14 54 3.0 9.5 x 1180 MPa grade  30 1032 23 32 2.0 10.4 ∘ 980 MPa grade 31 1144 13 42 0.5 10.1 x 980 MPa grade

TABLE 7 Composite microstructure High-temper- Low-temper- ature-formed ature-formed Polygonal Polygonal ferrite Retained Number bainite“a” bainite“b” ferrite “c” Total area Grain austenite percentage (in area (in area (in area percentage size Evalua- (in volume of MA No. percent) percent) percent) (a + b + c) (μm) tion percent) constituent 32 40 17 31 88 4 ∘ 15 ∘ 33 34 15 39 88 4 ∘ 15 ∘ 34 44 6 32 82 4 ∘ 16 x 35 38 24 28 90 4 ∘ 15 ∘ 36 26 32 29 87 8 ∘ 14 ∘ 37 46 45 0 91 — — 13 ∘ 38 39 37 12 88 4 ∘ 13 ∘ 39 32 30 25 87 4 ∘ 16 ∘ 40 21 27 38 86 14 Δ 14 ∘ 41 0 0 87 87 22 Δ 0 ∘ 42 28 37 26 91 5 ∘ 14 ∘ 43 22 35 33 90 5 ∘ 14 ∘ 44 22 41 31 94 4 ∘ 8 ∘ 45 21 41 25 87 3 ∘ 13 ∘ 46 35 23 41 99 2 ∘ 3 ∘ 47 23 31 38 92 4 ∘ 13 ∘ 48 4 29 63 96 15 Δ 8 ∘ 49 26 43 22 91 2 ∘ 12 ∘ 50 18 37 35 90 2 ∘ 13 ∘ 51 37 28 24 89 2 ∘ 13 ∘ 52 31 8 26 65 3 ∘ 7 x 53 25 32 33 90 4 ∘ 14 ∘ 54 29 38 24 91 4 ∘ 12 ∘ 55 16 53 22 91 3 ∘ 10 ∘ 56 21 48 23 92 4 ∘ 8 ∘ 57 18 29 47 94 8 ∘ 9 ∘ 58 28 41 24 93 3 ∘ 11 ∘ TS EL λ R Erichsen No. (MPa) (%) (%) (mm) value (mm) Assessment Remarks 32 998 25 26 2.5 10.7 ∘  980 MPa grade 33 1056 22 31 2.0 10.4 ∘  980 MPa grade 34 1116 19 20 3.0 9.5 x  980 MPa grade 35 986 24 27 2.5 10.6 ∘  980 MPa grade 36 1011 23 26 2.5 10.5 ∘  980 MPa grade 37 1025 18 62 0.0 10.3 x  980 MPa grade 38 985 24 35 1.5 10.5 ∘  980 MPa grade 39 1034 24 28 2.0 10.5 ∘  980 MPa grade 40 1022 21 34 0.0 10.2 ∘  980 MPa grade 41 689 22 34 0.0 10.6 x — 42 1032 23 32 0.5 10.4 ∘  980 MPa grade 43 1223 17 29 3.0 10.2 ∘ 1180 MPa grade 44 1295 15 31 4.0 9.8 ∘ 1270 MPa grade 45 1236 16 37 2.5 10.1 ∘ 1180 MPa grade 46 989 15 31 3.0 9.7 x  980 MPa grade 47 1188 18 36 3.0 10.2 ∘ 1180 MPa grade 48 994 16 39 2.5 10.2 x  980 MPa grade 49 1197 18 32 3.0 10.2 ∘ 1180 MPa grade 50 1191 19 29 3.5 10.3 ∘ 1180 MPa grade 51 1224 17 27 3.5 10.0 ∘ 1180 MPa grade 52 1489 9 16 6.0 9.1 x — 53 1192 19 25 4.0 10.2 ∘ 1180 MPa grade 54 1242 16 32 3.5 9.9 ∘ 1180 MPa grade 55 1315 15 34 4.5 9.7 ∘ 1270 MPa grade 56 1336 14 36 4.0 9.8 ∘ 1270 MPa grade 57 1285 14 41 4.0 9.6 ∘ 1270 MPa grade 58 1228 16 36 2.5 10.1 ∘ 1180 MPa grade

TABLE 8 Composite microstructure High-temper- Low-temper- ature-formed ature-formed Polygonal Polygonal ferrite Retained Number bainite“a” bainite“b” ferrite “c” Total area Grain austenite percentage (in area (in area (in area percentage size Evalua- (in volume of MA No. percent) percent) percent) (a + b + c) (μm) tion percent) constituent 59 26 43 21 90 2 ∘ 11 ∘ 60 32 23 42 97 4 ∘ 3 ∘ 61 0 0 97 97 22 Δ 0 ∘ 62 22 27 48 97 4 ∘ 3 ∘ 63 32 3 53 88 2 ∘ 12 x 64 28 33 28 89 2 ∘ 13 ∘ 65 22 35 32 89 3 ∘ 12 ∘ 66 24 33 34 91 5 ∘ 13 ∘ 67 27 38 22 87 5 ∘ 14 ∘ 68 23 38 28 89 5 ∘ 13 ∘ 69 22 35 31 88 5 ∘ 12 ∘ 70 25 36 29 90 4 ∘ 13 ∘ TS EL λ R Erichsen No. (MPa) (%) (%) (mm) value (mm) Assessment Remarks 59 1289 15 32 4.5 9.9 ∘ 1270 MPa grade 60 812 20 32 0.0 10.2 x  780 MPa grade 61 756 15 31 0.0 10.4 x — 62 854 19 38 0.0 10.2 x  780 MPa grade 63 877 19 13 0.5 10.0 x  780 MPa grade 64 1195 17 27 3.5 10.2 ∘ 1180 MPa grade 65 1224 17 25 3.0 10.3 ∘ 1180 MPa grade 66 1182 18 24 3.5 10.4 ∘ 1180 MPa grade 67 1256 18 29 4.0 10.0 ∘ 1180 MPa grade 68 1227 17 35 3.5 10.2 ∘ 1180 MPa grade 69 1216 18 24 3.5 10.4 ∘ 1180 MPa grade 70 1229 17 31 3.0 10.3 ∘ 1180 MPa grade

Experimental Example 2

Experimental slabs were prepared by subjecting steels having chemical compositions given in Table 9 below (with the remainder consisting of iron and inevitable impurities other than P, S, N, and O) to vacuum ingot making. The rare-earth elements (REM) in Table 9 employed a misch metal containing about 50% of La and about 30% of Ce.

The Ac₁ points and the Ac₃ points of the steels (slabs) were calculated based on the chemical compositions given in Table 9 and on Expression (a) and Expression (b), respectively. The results are indicated in Tables 10 and 11 below.

The prepared experimental slabs were sequentially subjected to hot rolling, cold rolling, and continuous annealing and yielded specimens. Specific conditions are as follows.

The experimental slabs were heated to 1250° C. and held at this temperature for 30 minutes, hot-rolled to a rolling reduction of about 90% at a finishing mill delivery temperature of 920° C., and cooled from this temperature down to a coiling temperature of 500° C. at an average cooling rate of 30° C. per second, and coiled. After being coiled, the works were held at the coiling temperature (500° C.) for 30 minutes, cooled down to room temperature through furnace cooling, and yielded hot-rolled steel sheets having a thickness of 2.6 mm.

The resulting hot-rolled steel sheets were subjected to acid wash to remove surface scales, cold-rolled to a cold rolling reduction of 46%, and yielded cold-rolled steel sheets having a thickness of 1.4 mm.

The resulting cold-rolled steel sheets were heated to temperatures (° C.) given in Tables 10 and 11, held for durations given in Tables 10 and 11 for soaking, cooled according to any of the following four patterns, subjected to continuous annealing, and yielded specimens.

Cooling Pattern i: corresponding to the pattern (i) in FIG. 3

After the soaking, a work was cooled down to a start temperature T (° C.) given in Tables 10 and 11 at an average cooling rate (° C. per second) given in Tables 10 and 11, held at this start temperature T (° C.), then cooled down to a start temperature (° C.) in the temperature range T2 given in Tables 10 and 11, and held at this start temperature. Tables 10 and 11 indicate a residence time (second) in the temperature range T1; and a residence time (second) in the temperature range T2. The tables also indicate a time (second) from the time point at which holding in the temperature range T1 was completed to the time point at which the work temperature reached the start temperature in the temperature range T2.

Cooling Pattern ii: corresponding to the pattern (ii) in FIG. 3

After the soaking, a work was cooled down to a start temperature T (° C.) given in Tables 10 and 11 at an average cooling rate (° C. per second) given in Tables 10 and 11, subsequently cooled down to an end temperature (° C.) given in Tables 10 and 11, cooled down to a start temperature (° C.) in the temperature range T2 given in Tables 10 and 11, and held at this start temperature for a duration (second) given in Tables 10 and 11. Tables 10 and 11 indicate a residence time (second) in the temperature range T1; and a residence time (second) in the temperature range T2. The tables also indicate a time (second) from the time point at which holding in the temperature range T1 was completed to the time point at which the work temperature reached the start temperature in the temperature range T2.

Cooling Pattern iii: corresponding to the pattern (iii) in FIG. 3

After the soaking, a work was cooled down to a start temperature T (° C.) given in Tables 10 and 11 at an average cooling rate (° C. per second) given in Tables 10 and 11, then cooled down to a start temperature (° C.) in the temperature range T2 given in Tables 10 and 11, and held at this start temperature. Tables 10 and 11 indicate a residence time (second) in the temperature range T1; and a residence time (second) in the temperature range T2.

Cooling Pattern iv

After the soaking, a work was cooled down to a start temperature (° C.) in the temperature range T1 given in Table 10 and held at the start temperature. Specifically, Sample No. 19 in Table 10 was a sample, in which the work after the soaking was held at 420° C. for 450 seconds and then cooled down to room temperature at an average cooling rate of 5° C. per second without holding (without stopping). The residence time in the temperature range T2 of this sample in Table 10 refers to a time necessary to pass through the temperature range T2. Table 10 indicates a residence time in the temperature range T1 (second) and a residence time in the temperature range T2 (second).

Of the start temperatures and the end temperatures in the temperature range T1; and of the start temperatures in the temperature range T2 given in Table 10, each of the asterisked values was out of the temperature range T1 or the temperature range T2 as specified in the present invention, but was indicated as a temperature in each column for convenience of explanation of the heat pattern.

The prepared specimens were subjected to metal structure observation and mechanical properties evaluation according to the following procedures.

Metal Structure Observation

Of the metal structure, area percentages of the polygonal ferrite, the high-temperature-formed bainite, and the low-temperature-formed bainite or the like (namely, the low-temperature-formed bainite and the tempered martensite) were calculated based on an observation with a scanning electron microscope (SEM); whereas a volume percentage of the retained austenite was determined by a saturation magnetization measurement.

(1) Area Percentages of Polygonal Ferrite, High-Temperature-Formed Bainite, and Low-Temperature-Formed Bainite and the Like

To determine these area percentages, a specimen cross section parallel to the rolling direction was surface-polished, further electropolished, etched with a Nital solution, and a position at a one-fourth depth the sheet thickness was observed in five view fields with a SEM at a 3000-fold magnification. One view field to be observed had a size of about 50 μm long by about 50 μm wide.

Next, average distances of retained austenite and carbides observed as white or pale gray microstructures in the observation view fields were measured according to the method mentioned above. The high-temperature-formed bainite and the low-temperature-formed bainite or the like were distinguished from each other by the average distance, whose area percentages were measured by point counting.

Tables 12 and 13 indicate an area percentage “a” (%) of the polygonal ferrite, an area percentage “b” (%) of the high-temperature-formed bainite, and a total area percentage “c” (%) of the low-temperature-formed bainite and the tempered martensite. The tables also indicate a total area percentage (a+b+c) of the area percentage “a”, the area percentage “b”, and the total area percentage “c”.

Equivalent circle diameters of polygonal ferrite grains observed in the observation view fields were measured and averaged. The results are indicated in Tables 12 and 13. In addition, a sample having an average equivalent circle diameter D of polygonal ferrite grains of 10 μm or less was evaluated as “∘” (good), and one having an average equivalent circle diameter of greater than 10 μm was evaluated as “Δ” (fair). The evaluation results are indicated in Tables 12 and 13.

(2) Retained Austenite Volume Percentage

Of the metal structure, a volume percentage of the retained austenite was determined by a saturation magnetization measurement. Specifically, a saturation magnetization (I) of a specimen and a saturation magnetization (Is) of a standard specimen were measured, based on which a volume percentage (Vγr) of the retained austenite was determined according to an expression below. The standard specimen had been subjected to a heat treatment at 400° C. for 15 hours. The saturation magnetization measurement was performed at room temperature with a DC magnetization B-H curve automatic recorder “Model BHS-40” supplied by Riken Denshi, Co., Ltd. with a maximum applied magnetization of 5000 (Oe). The expression is expressed as follows:

Vγr=(1−I/Is)×100

Equivalent circle diameters “d” of martensite-austenite constituents including both retained austenite and as-quenched martensite in combination were measured by polishing a surface of a specimen cross section parallel to the rolling direction, and observing the polished surface in five view fields with an optical microscope at a 1000-fold observation magnification. A number percentage of martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm with respect to the total number of the entire martensite-austenite constituents in the observed cross-section was calculated. A specimen having a number percentage of less than 15% was evaluated as accepted (∘), whereas a specimen having a number percentage of 15% or more was evaluated as rejected (x). The evaluation results are indicated in Tables 12 and 13.

Mechanical Properties Evaluation

Mechanical properties of each specimen were evaluated based on the tensile strength (TS), elongation (EL), bore expansion ratio (X), critical bending radius (R), and Erichsen value.

(1) The tensile strength (TS) and elongation (EL) were measured through a tensile test according to JIS Z 2241. As a test specimen, a JIS Z 2201 No. 5 test specimen was cut from the specimen so that a direction perpendicular to the specimen rolling direction be a longitudinal direction of the test specimen. The measurement results are indicated in Tables 12 and 13.

(2) Stretch flangeability was evaluated based on the bore expansion ratio. The bore expansion ratio (λ) was measured through a bore expanding test according to the Japan Iron and Steel Federation Standard (JFS) T 1001. The measurement results are indicated in Tables 12 and 13.

(3) The critical bending radius (R) was measured through a V-bending test according to JIS Z 2248. As a test specimen, a JIS Z 2204 No. 1 test specimen (thickness: 1.4 mm) was cut from the specimen so that a direction perpendicular to the specimen rolling direction be a longitudinal direction of the test specimen (i.e., so that the bend line agree with the rolling direction). The V-bending test was performed after applying mechanical grinding to a longitudinal end face of the test specimen so as to prevent cracking.

The V-bending test was performed at an angle between a die and a punch of 90° and at a punch tip radius varying in units of 0.5 mm. A minimum punch tip radius at which the test specimen can be bent without cracking was determined as the critical bending radius (R). The measurement results are indicated in Tables 12 and 13. The presence/absence of cracking was observed with a magnifying glass, and a test specimen without the occurrence of hair crack was evaluated as suffering from no cracking.

(4) The Erichsen value was measured through an Erichsen test according to JIS Z 2247. A test specimen of a size of 90 mm long by 90 mm wide by 1.4 mm thick was prepared by cutting from the specimen. The Erichsen test was performed with a device having a punch diameter of 20 mm. The measurement results are indicated in Tables 12 and 13. The Erichsen test enables evaluations of both the total elongation properties and the local ductility of the steel sheet.

The mechanical properties of the specimen were evaluated based on criteria for the elongation (EL), bore expansion ratio (X), critical bending radius (R), and Erichsen value varying depending on the tensile strength (TS). Specifically, required properties including EL, λ, R, and Erichsen value vary depending on the steel sheet tensile strength TS. Accordingly, the mechanical properties were evaluated in accordance with the following criteria that vary depending on the TS level.

Based on the criteria, a sample evaluated as satisfactory all in the properties of EL, λ, R, and Erichsen value were evaluated as accepted (∘), whereas a sample having one or more properties lower than the criteria was evaluated as rejected (x). The evaluation results are indicated in Tables 12 and 13.

-   -   (1) TS of 590 MPa grade

TS: from 590 MPa to less than 780 MPa

EL: 34% or more

λ: 30% or more

R: 0.5 mm or less

Erichsen value: 10.8 mm or more

-   -   (2) TS of 780 MPa grade

TS: from 780 MPa to less than 980 MPa

EL: 25% or more

λ: 30% or more

R: 1.0 mm or less

Erichsen value: 10.4 mm or more

-   -   (3) TS of 980 MPa grade

TS: from 980 MPa to less than 1180 MPa

EL: 19% or more

λ: 20% or more

R: 3.0 mm or less

Erichsen value: 10.0 mm or more

-   -   (4) TS of 1180 MPa grade

TS: from 1180 MPa to less than 1270 MPa

EL: 15% or more

λ: 20% or more

R: 4.5 mm or less

Erichsen value: 9.6 mm or more

The second high-strength steel sheet is designed to be applied to steel sheets having a tensile strength TS of from 590 MPa to less than 1270 MPa. Samples having a tensile strength TS of less than 590 MPa, or of 1270 MPa or more were ineligible herein even when being satisfactory in EL, λ, R, and Erichsen value.

Tables 9 to 13 demonstrate as follows. Of Samples Nos. 1 to 43 in Tables 12 and 13, Samples Nos. 1, 3, 4, 11, 14, 15, 20, and 28 underwent cooling in Pattern i; Samples Nos. 2 and 6 underwent cooling in Pattern iii; Sample No. 19 underwent cooling in Pattern iv; and the other samples underwent cooling in Pattern

Samples evaluated as “o” in the assessment in Tables 12 and 13 were steel sheets satisfying the conditions specified in the present invention and satisfying criteria values of the mechanical properties (EL, λ, R, and Erichsen value) determined according to the tensile strength TS. This demonstrates that high-strength steel sheets according to the present invention had a high elongation and satisfactory local formability and exhibited good workability in general.

By contrast, samples evaluated as “x” in the assessment (Samples Nos. 4, 8, 9, 12, 15, 18 to 20, 31, and 34 to 36 in Tables 12 and 13) were steel sheets not satisfying one or more of the conditions specified in the present invention. Details thereof are as follows.

Sample No. 4 in Table 12 underwent, after being heated to and held in the two-phase temperature range, cooling down to an arbitrary temperature T falling within the range specified by Expression (1) at an excessively low average cooling rate. This sample suffered from pearlite transformation, failed to include a desired amount of the retained austenite, and thereby had an insufficient strength. Sample No. 8 in Table 12 underwent holding in the two-phase temperature range for an excessively short time. This sample failed to include a sufficient amount of the retained austenite and had an insufficient strength. Sample No. 9 in Table 12 underwent, after the soaking, holding at a temperature higher than the temperature range T1 specified in the present invention, subsequently cooling down to the temperature range T2 without holding in the temperature range T1, and holding in the temperature range T2. This sample suffered from heavy formation of polygonal ferrite and suffered from formation of insufficient amounts of the high-temperature-formed bainite and the retained austenite. The sample had an elongation and a Erichsen value at low levels and failed to exhibit better workability.

Sample No. 12 in Table 12 underwent, after holding in the temperature range T1, cooling down to a temperature lower than the temperature range T2 without holding in the temperature range T2. This sample suffered from little formation of the low-temperature-formed bainite, included a large amount of coarse martensite-austenite constituents as identified through SEM observation, and included a large amount of as-quenched martensite. The sample satisfied none of the specified acceptance criteria in elongation, bore expansion ratio, critical bending radius, and Erichsen value and failed to exhibit better workability. Sample No. 15 in Table 12 underwent holding in the temperature range T1 for an excessively long time without holding in the temperature range T2. This sample suffered from insufficient formation of the low-temperature-formed bainite or the like and heavy formation of coarse martensite-austenite constituents. The sample therefore have a low bore expansion ratio, a small critical bending radius, and a low Erichsen value to have poor local formability and failed to exhibit better steel sheet workability.

Sample No. 18 in Table 12 underwent heating at an excessively high temperature, thereby suffered from little formation of polygonal ferrite and excessive formation of the high-temperature-formed bainite and the low-temperature-formed bainite or the like. This sample had a low elongation and failed to exhibit better steel sheet workability. Sample No. 19 in Table 12 underwent holding in the temperature range T1 for an excessively long time, and cooling without holding in the temperature range T2. This sample suffered from insufficient formation of the low-temperature-formed bainite or the like and heavy formation of coarse martensite-austenite constituents. The sample had a low bore expansion ratio and a low Erichsen value to have poor local formability and failed to exhibit better workability. Sample No. 20 in Table 12 underwent, after the soaking, cooling down to the temperature range T2 without holding in the temperature range T1(without stopping), and holding at two different temperatures in the temperature range T2. This sample suffered from little formation of the high-temperature-formed bainite and little formation of the retained austenite because of being held only in the temperature range T2. The sample had an elongation and an Erichsen value at low levels and failed to exhibit better workability. Sample No. 31 in Table 13 underwent heating at an excessively low temperature. This sample suffered from heavy formation of polygonal ferrite and no formation of the high-temperature-formed bainite, the low-temperature-formed bainite or the like, and the retained austenite. The sample had a low elongation and failed to exhibit better workability.

Sample No. 34 in Table 13 had an excessively low carbon content. This sample suffered from insufficient formation of the retained austenite, had an elongation and an Erichsen value at low levels, and failed to exhibit better workability. Sample No. 35 in Table 13 had an excessively low Si content. This sample suffered from insufficient formation of the retained austenite, had a low elongation, and failed to exhibit better workability. Sample No. 36 in Table 13 had an excessively low Mn content and underwent insufficient quenching. This sample underwent accelerated formation of polygonal ferrite during cooling, but suffered from insufficient formation of the low-temperature-formed bainite or the like. The sample had an elongation, a bore expansion ratio, and a critical bending radius at low levels and failed to exhibit better workability.

These results demonstrate that the present invention can provide high-strength steel sheets exhibiting better workability.

Steel sheets having a tensile strength of 780 MPa grade are indicated in Tables 12 and 13. Among them, Samples Nos. 3, 5 to 7, 11, 14, 16, 17, 23 to 26, 30, 32, and 37 to 43 satisfied the conditions specified in the present invention. Relating to these samples, a relationship between the elongation (EL) and the tensile strength (TS) is illustrated in FIG. 5. In FIG. 5, data indicated by the symbol “” (filled circle) are data of samples having an average equivalent circle diameter D of polygonal ferrite grains of 10 μm or less; and data indicated by the symbol “▪” (filled square) are data of samples having an average equivalent circle diameter D of polygonal ferrite grains of greater than 10 μm.

FIG. 5 demonstrates that steel sheets could have a higher elongation (EL) and exhibit further better workability by controlling the average equivalent circle diameter D of polygonal ferrite grains to 10 μm or less, even when having a tensile strength (TS) at an equivalent level.

TABLE 9 Steel Chemical composition (in mass percent) type C Si Mn P S Al Cr Mo Ti Nb V Cu Ni B Ca Mg REM N O A 0.11 1.32 1.57 0.02 0.002 0.02 — — — — — — — — — — — 0.002 0.001 B 0.14 1.82 2.29 0.02 0.001 0.04 — — — — — — — — — — — 0.004 0.001 C 0.10 1.13 2.05 0.01 0.002 0.05 — — — — — — — — — — — 0.002 0.002 D 0.19 2.54 2.38 0.03 0.001 0.04 — — — — — — — — — — — 0.005 0.002 E 0.18 1.54 2.01 0.01 0.002 0.05 — — — — — — — — — — — 0.004 0.002 F 0.16 1.55 1.63 0.03 0.001 0.02 0.4 — — — — — — — — — — 0.003 0.002 G 0.16 1.58 1.66 0.03 0.001 0.04 — 0.3 — — — — — — — — — 0.004 0.001 H 0.16 1.54 1.87 0.02 0.001 0.03 — — 0.07 — — — — — — — — 0.005 0.002 I 0.17 1.56 1.88 0.02 0.002 0.03 — — 0.02 0.04 — — — — — — — 0.005 0.001 J 0.16 1.17 1.85 0.02 0.001 0.45 — — — — 0.08 — — — — — — 0.003 0.001 K 0.27 1.88 2.04 0.02 0.002 0.03 — — — — — 0.24 0.28 — — — — 0.002 0.002 L 0.15 2.48 1.91 0.02 0.002 0.02 — — 0.02 — — — — 0.0025 — — — 0.005 0.002 M 0.23 1.18 2.47 0.02 0.002 1.03 — — — — — — — — — — — 0.002 0.002 N 0.20 2.05 2.25 0.01 0.001 0.02 — — — — — — — — 0.0021 0.0012 0.0018 0.003 0.002 O 0.07 1.54 2.08 0.01 0.001 0.05 — — — — — — — — — — — 0.003 0.002 P 0.18 0.56 1.87 0.02 0.002 0.04 — — — — — — — — — — — 0.003 0.001 Q 0.18 1.84 0.84 0.02 0.001 0.05 — — — — — — — — — — — 0.002 0.001 R 0.16 1.60 1.87 0.02 0.001 0.02 — — — 0.06 — — — — — — — 0.002 0.002 S 0.16 1.56 1.89 0.02 0.001 0.05 — — — — — 0.06 — — — — — 0.003 0.002 T 0.16 1.58 1.85 0.02 0.001 0.04 — — — — — — 0.47 — — — — 0.002 0.001 U 0.16 1.58 1.86 0.03 0.001 0.03 — — — — — — — 0.0006 — — — 0.003 0.001 V 0.16 1.57 1.86 0.01 0.001 0.02 — — — — — — — — 0.0022 — — 0.004 0.001 W 0.16 1.58 1.86 0.01 0.001 0.03 — — — — — — — — — 0.0019 — 0.003 0.002 X 0.17 1.59 1.88 0.01 0.001 0.05 — — — — — — — — — — 0.0024 0.002 0.001

TABLE 10 Soaking Heating Holding Average Steel Ac₁ Ac₃ Ac₁ + 20 Ac₃ + 20 temperature time cooling rate No. type (° C.) (° C.) (° C.) (° C.) (° C.) (sec) (° C./sec) 1 A 745 878 765 898 860 200 15 2 A 745 878 765 898 860 60 15 3 A 745 878 765 898 860 200 45 4 A 745 878 765 898 860 200 1 5 B 751 877 771 897 840 200 15 6 B 751 877 771 897 840 200 5 7 B 751 877 771 897 840 200 15 8 B 751 877 771 897 860 20 10 9 B 751 877 771 897 860 200 15 10 C 734 861 754 881 820 200 15 11 C 734 861 754 881 820 200 15 12 C 734 861 754 881 840 200 10 13 D 771 901 791 921 860 200 15 14 D 771 901 791 921 890 490 10 15 D 771 901 791 921 860 200 15 16 E 746 860 766 880 840 200 15 17 E 746 860 766 880 840 200 15 18 E 746 860 766 880 900 200 45 19 E 746 860 766 880 820 200 15 20 E 746 860 766 880 820 200 20 Temper- Temperature ature range T1 range T2 Residence Start End Time Start time (sec) temper- temper- from T1 temper- Temper- Temper- ature T ature to T2 ature ature ature Cooling No. (° C.) (° C.) (sec) (° C.) range T1 range T2 pattern 1 420 420 4 380 75 488 i 2 420 — — 380 33 515 iii 3 420 420 4 350 29 483 i 4 420 420 4 350 146 483 i 5 450 420 4 350 32 483 ii 6 450 — — 320 28 493 iii 7 520 490 4 350 29 481 ii 8 450 420 4 380 36 488 ii 9   650    620  4 380 4 486 ii 10 450 420 4 380 33 488 ii 11 410 410 4 320 34 478 i 12 450   380  4   150  27 11 ii 13 450 420 4 290 12 471 ii 14 480 480 4 380 34 487 i 15 480 480 4   420  483 40 i 16 450 420 4 320 32 477 ii 17 450 420 20  230 33 1824 ii 18 450 420 4 380 29 488 ii 19 420 420 — — 462 40 iv 20   380    380  4 350 7 510 i

TABLE 11 Soaking Heating Holding Average Steel Ac₁ Ac₃ Ac₁ + 20 Ac₃ + 20 temperature time cooling rate No. type (° C.) (° C.) (° C.) (° C.) (° C.) (sec) (° C./sec) 21 F 757 874 777 894 840 200 15 22 G 751 897 771 917 840 200 15 23 H 748 895 768 915 860 200 15 24 H 748 895 768 915 860 200 15 25 I 748 875 768 895 860 200 15 26 J 737 1027 757 1047 840 200 15 27 K 751 844 771 864 780 200 15 28 K 751 844 771 864 820 200 30 29 L 775 912 795 932 880 200 15 30 L 775 912 795 932 910 480 10 31 L 775 912 795 932 750 200 15 32 M 731 1218 751 1238 820 200 15 33 N 759 858 779 878 820 200 15 34 O 746 891 766 911 840 200 15 35 P 719 824 739 844 800 200 15 36 Q 768 915 788 935 840 200 15 37 R 750 867 770 887 840 200 15 38 S 748 875 768 895 840 200 15 39 T 741 868 761 888 840 200 15 40 U 749 877 769 897 840 200 15 41 V 749 859 769 879 840 200 15 42 W 749 862 769 882 840 200 15 43 X 749 869 769 889 840 200 15 Temper- Temperature ature range T1 range T2 Residence Start End Time Start time (sec) temper- temper- from T1 temper- Temper- Temper- ature T ature to T2 ature ature ature Cooling No. (° C.) (° C.) (sec) (° C.) range T1 range T2 pattern 21 450 420 4 350 32 483 ii 22 450 420 4 380 33 488 ii 23 450 420 4 350 32 483 ii 24 450 420 4 350 32 233 ii 25 450 420 4 350 32 483 ii 26 450 420 4 350 32 483 ii 27 450 420 4 230 31 910 ii 28 420 420 4 380 86 938 i 29 450 420 4 320 32 477 ii 30 480 450 4 380 34 487 ii 31 450 420 4 320 32 477 ii 32 450 420 4 350 32 1233 ii 33 450 420 4 320 32 477 ii 34 450 420 4 350 32 483 ii 35 450 420 4 350 32 483 ii 36 450 420 4 350 32 483 ii 37 450 420 4 350 32 483 ii 38 450 420 4 350 32 483 ii 39 450 420 4 350 32 483 ii 40 450 420 4 350 32 483 ii 41 450 420 4 350 32 483 ii 42 450 420 4 350 32 483 ii 43 450 420 4 350 32 483 ii

TABLE 12 Composite microstructure High-temper- Low-temper- Polygonal ature-formed ature-formed Polygonal ferrite Retained Number ferrite “a” bainite“b” bainite“c” Total area Grain austenite percentage (in area (in area (in area percentage size Evalua- (in volume of MA No. percent) percent) percent) (a + b + c) (μm) tion percent) constituent 1 81 6 10 97 5 ∘ 6 ∘ 2 68 11 16 95 4 ∘ 7 ∘ 3 63 12 17 92 5 ∘ 10 ∘ 4 78 0 0 78 5 ∘ 0 ∘ 5 65 11 18 94 4 ∘ 11 ∘ 6 75 7 10 92 4 ∘ 12 ∘ 7 66 14 13 93 5 ∘ 11 ∘ 8 75 15 8 98 5 ∘ 2 ∘ 9 72 3 21 96 15 Δ 4 ∘ 10 74 8 12 94 4 ∘ 7 ∘ 11 78 11 8 97 4 ∘ 6 ∘ 12 68 7 3 78 5 ∘ 5 x 13 62 7 22 91 5 ∘ 15 ∘ 14 64 11 18 93 14 Δ 10 ∘ 15 61 18 3 82 5 ∘ 9 x 16 71 9 13 93 4 ∘ 10 ∘ 17 74 7 15 96 5 ∘ 9 ∘ 18 6 45 41 92 4 ∘ 10 ∘ 19 73 11 2 86 4 ∘ 14 x 20 62 4 33 99 4 ∘ 3 ∘ TS EL λ R Erichsen No. (MPa) (%) (%) (mm) value (mm) Assessment Remarks 1 626 36 54 0.0 11.3 ∘ 590 MPa grade 2 654 35 45 0.0 11.2 ∘ 590 MPa grade 3 835 29 45 0.0 10.7 ∘ 780 MPa grade 4 559 23 46 0.0 10.1 x — 5 822 31 37 0.5 10.9 ∘ 780 MPa grade 6 808 31 39 0.0 11.0 ∘ 780 MPa grade 7 818 30 41 0.5 10.8 ∘ 780 MPa grade 8 562 25 36 0.0 10.2 x — 9 615 31 44 0.0 10.5 x 590 MPa grade 10 638 36 56 0.0 11.4 ∘ 590 MPa grade 11 801 31 45 0.0 11.0 ∘ 780 MPa grade 12 937 17 26 1.5 10.1 x 780 MPa grade 13 1035 22 26 1.5 10.4 ∘ 980 MPa grade 14 822 28 41 0.5 10.7 ∘ 780 MPa grade 15 908 25 20 1.5 10.1 x 780 MPa grade 16 785 32 38 0.0 11.0 ∘ 780 MPa grade 17 848 28 35 0.5 10.8 ∘ 780 MPa grade 18 1001 17 63 0.0 10.7 x 980 MPa grade 19 996 23 17 2.5 9.8 x 980 MPa grade 20 1139 16 52 1.5 9.9 x 980 MPa grade

TABLE 13 Composite microstructure High-temper- Low-temper- Polygonal ature-formed ature-formed Polygonal ferrite Retained Number ferrite “a” bainite“b” bainite“c” Total area Grain austenite percentage (in area (in area (in area percentage size Evalua- (in volume of MA No. percent) percent) percent) (a + b + c) (μm) tion percent) constituent 21 57 8 22 87 5 ∘ 15 ∘ 22 69 6 14 89 4 ∘ 11 ∘ 23 76 7 9 92 2 ∘ 11 ∘ 24 75 7 11 93 2 ∘ 10 ∘ 25 65 15 13 93 2 ∘ 9 ∘ 26 73 12 9 94 3 ∘ 10 ∘ 27 55 8 27 90 3 ∘ 11 ∘ 28 56 13 10 79 5 ∘ 12 ∘ 29 59 15 14 88 5 ∘ 13 ∘ 30 65 13 14 92 12 Δ 9 ∘ 31 88 0 0 88 22 Δ 0 ∘ 32 69 7 12 88 5 ∘ 16 ∘ 33 53 10 23 86 5 ∘ 16 ∘ 34 75 5 15 95 4 ∘ 2 ∘ 35 66 8 24 98 22 Δ 3 ∘ 36 82 14 2 98 5 ∘ 7 ∘ 37 71 8 12 91 4 ∘ 11 ∘ 38 75 9 9 93 5 ∘ 10 ∘ 39 68 6 17 91 5 ∘ 12 ∘ 40 72 6 14 92 4 ∘ 12 ∘ 41 71 7 13 91 5 ∘ 10 ∘ 42 74 9 11 94 5 ∘ 11 ∘ 43 72 7 12 91 4 ∘ 10 ∘ TS EL λ Erichsen No. (MPa) (%) (%) R(mm) value (mm) Assessment Remarks 21 1004 23 34 2.0 10.6 ∘ 980 MPa grade 22 1028 23 28 1.5 10.5 ∘ 980 MPa grade 23 834 29 43 0.0 10.9 ∘ 780 MPa grade 24 842 29 35 0.5 10.8 ∘ 780 MPa grade 25 854 28 36 0.0 10.7 ∘ 780 MPa grade 26 797 31 44 0.0 11.0 ∘ 780 MPa grade 27 1194 18 33 1.0 10.0 ∘ 1180 MPa grade  28 1032 22 23 2.0 10.2 ∘ 980 MPa grade 29 1027 22 25 2.0 10.5 ∘ 980 MPa grade 30 792 30 44 0.0 10.7 ∘ 780 MPa grade 31 626 23 48 0.0 11.0 x 590 MPa grade 32 854 28 35 0.5 10.8 ∘ 780 MPa grade 33 1024 22 26 2.0 10.5 ∘ 980 MPa grade 34 634 31 43 0.0 10.7 x 590 MPa grade 35 831 21 41 0.0 10.4 x 780 MPa grade 36 756 28 13 1.0 11.0 x 590 MPa grade 37 838 29 38 0.0 10.6 ∘ 780 MPa grade 38 821 30 35 0.0 10.7 ∘ 780 MPa grade 39 856 29 45 0.5 10.9 ∘ 780 MPa grade 40 823 30 38 0.0 10.7 ∘ 780 MPa grade 41 810 30 46 0.0 10.7 ∘ 780 MPa grade 42 801 31 38 0.5 10.8 ∘ 780 MPa grade 43 822 29 41 0.0 10.9 ∘ 780 MPa grade 

1. A high-strength steel sheet, comprising, by mass percent based on a total mass of the steel sheet, iron and: from 0.10% to 0.3% of C; from 1.0% to 3.0% of Si; from 1.5% to 3% of Mn; from 0.005% to 3% of Al; 0.1% or less of P; and 0.05% or less of S, wherein: the steel sheet has a metal structure comprising bainite, polygonal ferrite, retained austenite, and tempered martensite; (1) when the metal structure is observed with a scanning electron microscope, (1a) the bainite has a composite microstructure comprising: a high-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of 1 μm or more; and a low-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of less than 1 μm, the high-temperature-formed bainite is present in an area percentage “a” of from 10% to 80% of the entire metal structure; the low-temperature-formed bainite and the tempered martensite are present in a total area percentage “b” of from 10% to 80% of the entire metal structure; and (1b) the polygonal ferrite is present in an area percentage “c” of from 10% to 50% of the entire metal structure; and (2) the retained austenite is present in a volume percentage of 5% or more of the entire metal structure as determined by a saturation magnetization measurement.
 2. The high-strength steel sheet of claim 1, wherein, when martensite-austenite constituents comprising both as-quenched martensite and retained austenite are observed at a cross-section of the metal structure with an optical microscope, martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm are present in a number percentage of from 0% to less than 15% of a total number of the entire martensite-austenite constituents at the observed cross-section.
 3. The high-strength steel sheet of claim 1, wherein grains of the polygonal ferrite have an average equivalent circle diameter D of from greater than 0 μm to 10 μm.
 4. The high-strength steel sheet of claim 1, further comprising, by mass percent based on a total mass of the steel sheet: from greater than 0% to 1% of Cr; and/or from greater than 0% to 1% of Mo.
 5. The high-strength steel sheet of claim 1, further comprising, by mass percent based on a total mass of the steel sheet, at least one element selected from the group consisting of: from greater than 0% to 0.15% of Ti; from greater than 0% to 0.15% of Nb; and from greater than 0% to 0.15% of V.
 6. The high-strength steel sheet of claim 1, further comprising, by mass percent based on a total mass of the steel sheet: from greater than 0% to 1% of Cu; and/or from greater than 0% to 1% of Ni.
 7. The high-strength steel sheet of claim 1, further comprising, by mass percent based on a total mass of the steel sheet, from greater than 0% to 0.005% of B.
 8. The high-strength steel sheet of claim 1, further comprising, by mass percent based on a total mass of the steel sheet, at least one element selected from the group consisting of: from greater than 0% to 0.01% of Ca; from greater than 0% to 0.01% of Mg; and from greater than 0% to 0.01% of a rare-earth element.
 9. The high-strength steel sheet of claim 1, comprising a hot-dip galvanized layer or a hot-dip galvanized layer on a surface thereof.
 10. A method of manufacturing the high-strength steel sheet of claim 1, the method comprising, in the following order: heating a steel sheet to a temperature range of from [{(Ac₁ point+Ac₃ point)/2}+20° C.] to [Ac₃ point+20° C.]; holding the steel sheet in the temperature range for 50 seconds or longer; cooling the steel sheet down to an arbitrary temperature T at an average cooling rate of 2° C. or above per second, the temperature T falling within a range specified by Expression (1); holding the steel sheet in the temperature range specified by Expression (1) for 10 to 100 seconds; and holding the steel sheet in a temperature range specified by Expression (2) for 200 seconds or longer, wherein Expressions (1) and (2) are as follows: 400° C.≦T1(° C.)≦540° C.  (1) 200° C.≦T2(° C.)<400° C.  (2).
 11. A high-strength steel sheet, comprising, by mass percent based on a total mass of the steel sheet, iron and: from 0.10% to 0.3% of C; from 1.0% to 3% of Si; from 1.0% to 2.5% of Mn; from 0.005% to 3% of Al; 0.1% or less of P; and 0.05% or less of S, wherein: the steel sheet has a metal structure comprising polygonal ferrite, bainite, tempered martensite, and retained austenite; (1) when the metal structure is observed with a scanning electron microscope, (1a) the polygonal ferrite is present in an area percentage “a” of greater than 50% of the entire metal structure, (1b) the bainite has a composite microstructure comprising: a high-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of 1 μm or more; and a low-temperature-formed bainite having an average distance between adjacent regions of retained austenite and/or carbide of less than 1 μm, the high-temperature-formed bainite is present in an area percentage “b” of from 5% to 40% of the entire metal structure; and the low-temperature-formed bainite and the tempered martensite are present in a total area percentage “c” of from 5% to 40% of the entire metal structure; and (2) the retained austenite is present in a volume percentage of 5% or more of the entire metal structure as determined by a saturation magnetization measurement.
 12. The high-strength steel sheet of claim 11, wherein, when martensite-austenite constituents comprising both as-quenched martensite and retained austenite are observed at a cross-section of the metal structure with an optical microscope, martensite-austenite constituents each having an equivalent circle diameter “d” of greater than 7 μm are present in a number percentage of from 0% to less than 15% of a total number of entire martensite-austenite constituents at the observed cross-section.
 13. The high-strength steel sheet of claim 11, wherein grains of the polygonal ferrite have an average equivalent circle diameter D of from greater than 0 μm to 10 μm.
 14. The high-strength steel sheet of claim 11, further comprising, by mass percent based on a total mass of the steel sheet: from greater than 0% to 1% of Cr; and/or from greater than 0% to 1% of Mo.
 15. The high-strength steel sheet of claim 11, further comprising, by mass percent based on a total mass of the steel sheet, at least one element selected from the group consisting of: from greater than 0% to 0.15% of Ti; from greater than 0% to 0.15% of Nb; and from greater than 0% to 0.15% of V.
 16. The high-strength steel sheet of claim 11, further comprising, by mass percent based on a total mass of the steel sheet: from greater than 0% to 1% of Cu; and/or from greater than 0% to 1% of Ni.
 17. The high-strength steel sheet of claim 11, further comprising, by mass percent based on a total mass of the steel sheet, from greater than 0% to 0.005% of B.
 18. The high-strength steel sheet of claim 11, further comprising, by mass percent based on a total mass of the steel sheet, at least one element selected from the group consisting of: from greater than 0% to 0.01% of Ca; from greater than 0% to 0.01% of Mg; and from greater than 0% to 0.01% of a rare-earth element.
 19. The high-strength steel sheet of claim 11, comprising a hot-dip galvanized layer or a hot-dip galvannealed layer on a surface thereof.
 20. A method of manufacturing the high-strength steel sheet of claim 11, the method comprising, in the following order: heating a steel sheet to a temperature range of from [Ac₁ point+20° C.] to [Ac₃ point+20° C.]; holding the steel sheet in the temperature range for 50 seconds or longer; cooling the steel sheet down to an arbitrary temperature T at an average cooling rate of from 2° C. to 50° C. per second, the temperature T falling within a range specified by Expression (1); holding the steel sheet in the temperature range specified by Expression (1) for 10 to 100 seconds; and holding the steel sheet in a temperature range specified by Expression (2) for 200 seconds or longer, wherein Expressions (1) and (2) are as follows: 400° C.≦T1(° C.)≦540° C.  (1) 200° C.≦T2(° C.)<400° C.  (2). 